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31 (261)
Susana Barrios
From:Rick Moyer <dr.rickmoyer@gmail.com>
Sent:Monday,
To:Public Comment; Nicholas J. Taylor; Kristin Pelletier
Subject:\[EXTERNAL\] Local landslide information
Attachments:E and S 1996 Report Volume 1.pdf; Santiago_Landslide 2005 Study GRABEN.pdf
Some people who received this message don't often get email from Learn why this is important
Warning: This email originated from outside the City of Anaheim. Do not click links or open
attachments unless you recognize the sender and are expecting the message.
Dear Mayor Aitken and members of the City Council:
According to the Deer Canyon Geology and Soils Report, "There have been historic landslides within
eastern Anaheim. In 1993, the Santiago Landslide occurred following a major El Nino rain event a bluff
slid and prompted the evacuation of dozens of families. This event destroyed over 30 homes and
impacted over 200 other structures in the vicinity". Unfortunately this is a gross misrepresentation of the
Santiago Landslide which actually began in 1992. It is incomprehensible that such a misrepresentation
would occur in this day and age when there is so much information available about the Santiago
Landslide. This misrepresentation makes the entire Soils report suspect.
For example, in 2023 the City of Anaheim paid for an updated geotechnical report of the Santiago
landslide by Tetra-Tech. According to their engineers the landslide almost reactivated a couple of years
ago. They estimate that if our dewatering system shuts down (the current assessment sundowns and we
will run out of money in 2025), it will take about 18 months before we have another landslide. Below is a
link to their report. This report is also available on a website dedicated to the landslide that the City
maintains. Search Anaheim.net/SGHAD. The City of Anaheim is very involved with our landslide issue
and Mr. Emami personally attends most of the board meetings.
SGHAD Geotechnical Evaluation and Groundwater Impact Web 7-18-23.pdf
The main SGHAD website is www.santiagoghad.org. It has a lot of information, a good GIS map and is up
to date. There is a link to a video created by one of the homeowners a short time following the landslide.
In 1996 Eberhart and Stone published a 7 volume report about the Santiago landslide. I've attached
Volume 1 which provides great detail about the landslide and local geology, the other volumes contain
maps and technical information and are available along with many other documents on the SGHAD
website.
An interesting study about the landslide was published in 2005 for a professional journal, noting the
presence of a graben. The authors reviewed old aerial photos of the area (pre-development) and noted
the presence of the ancient landslide that was involved with the Santiago landslide (bottom right of page
12). It might be worth investigating whether or not the geotechnical consultants for the Deer Canyon
project reviewed aerial photography as part of their assessment. Had this been done by the pre-
1
development consultants in our area further up the hill, the City would have either not allowed any
development or mandated certain mitigation efforts to stabilize the earth prior to development.
ENGEO is the SGHAD manager, the President is Uri Eliahu (ueliahu@engeo.com). Best to all, Rick.
--
Dr. Rick Moyer
2
The Santiago Landslide and Associated Ridge-top
Graben (Sackungen): Implications for Paleoseismic
Landslide Studies
PHILIP L. JOHNSON
WILLIAM R. COTTON
Cotton, Shires & Associates, 330 Village Lane, Los Gatos, CA 95030
Key Terms:Ridge-top Graben, Sackungen, Landslide,
Paleoseismology, Rainfall
ABSTRACT
Some recent paleoseismic studies have focused on
datingridge-topgrabendepositstoevaluatethetiming
of paleoseismic events. By contrast, our study of the
Santiago landslide demonstrates that ridge-top gra-
bens also can be associated with aseismic, deep-seated
landsliding. The Santiago landslide in Anaheim Hills,
California, failed during the winter of 1992–1993 in
response to elevated groundwater conditions asso-
ciated with intense rainfall. The head of the active
landslide included a zone of extensional deformation
along the bounding ridgeline. Interpretation of histor-
ical, aerial photographs indicates that the active
landslide is a re-activated, ancient, deep-seated, trans-
lational landslide and an associated ridge-top graben.
Large-diameter borings within the ridge-top graben
encountered thick colluvium, steeply dipping colluvi-
um-filled fractures, and shears with normal offsets. In
contrast to the rupture surface within the central part
of the landslide, the basal rupture surfaces in the
graben area had significantly less gouge. We interpret
this contrast in gouge development as an indication
that the ridge-top graben developed later than the
original landslide by upslope progression of the
deformation. Our limit-equilibrium, slope-stability
analyses indicate that either high groundwater or
seismicgroundmotioncouldhavepreviouslyactivated
the ancient landslide and ridge-top graben. Because
colluvial deposits preserved within the ridge-top
graben and produced by these two different types of
triggeringeventscouldbemisinterpretedasrepresent-
ing the late Quaternary paleoseismic record, these
features are not useful for paleoseismic studies unless
aseismic activation can be clearly precluded.
INTRODUCTION
The Santiago landslide, located in the Anaheim Hills
area of the northern Santa Ana Mountains, California
(Figure 1), is an active landslide that produced extensional
deformation within the adjacent part of the upslope
bounding ridgeline. Initial movement of the landslide
causedminorcracksinroadsurfacesduring1992(Barrows
et al., 1993). This was followed in January 1993 by major
episodes of landslide movement following intense rainfall
in December 1992 and January 1993 (Slosson and Larson,
1995). Initial investigations (McLarty and Lancaster,
1999a) concluded that elevated groundwater conditions
triggered landslide movement and that the maximum
displacement was approximately 1 ft (0.3 m). A zone of
extensionalground cracks wasmappedalongthe ridgeline
at the head of the landslide in January 1993; these ground-
crackdatawereincorporatedintoourengineeringgeologic
map (Figure 2). Movementof the landslide andopening of
the associated ridge-top graben occurred during a seismi-
cally quiescent period when groundwater levels were ele-
vated (Barrows et al., 1993). Thus, re-activation was
related to groundwater conditions associated with intense
rainfall rather than strong seismic shaking.
There are several different interpretations for the origin
of ridge-top grabens (sackungen). Some have hypothe-
sized that sackungen develop by slow, gravitational defor-
mation of ridgelines (Tabor, 1971; Varnes et al., 1989;
Bovis and Evans, 1995; McCalpin and Irvine, 1995; and
Thompson, 1997). Others have interpreted sackungen de-
velopment as a response to loss of buttressing and to stress
relief associated with late Pleistocene deglaciation (Bovis,
1982; Agliardi et al., 2001; Kellogg, 2001a; and Smith,
2001). A third hypothesis is that these grabens open in
response to strong seismic shaking and ridge-top shatter
(Beck, 1968; Clague, 1979; Wallace, 1984; Morton and
Sadler, 1989; and Kellogg, 2001b). One argument for the
seismic origin of sackungen is the abundance of these
features in some regions with high rates of seismic activity
(Radbruch-Hall, 1978; Hart, 2001). Several studies in the
SantaCruzMountainsofnorthernCaliforniafollowingthe
1989 Loma Prieta earthquake (Ponti and Wells, 1991;
NolanandWeber,1998)reportedapparent,activeopening
of sackungen in response to strong seismic shaking.
McCalpin (1999) trenched across a ridge-top graben in
central Nevada that was active during two historical
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–15 5
earthquakes and found evidence of four prehistoric,
graben-openingeventsthattheauthorinterpretedaspaleo-
seismic in origin. McCalpin and Hart (2001) interpreted
sackungendepositsintheSanGabrielMountainsofsouth-
ern California as paleoseismic in origin and compared
graben-opening events with paleoseismic events recorded
at nearby fault trench sites.
Jibson(1996)suggestedthatsackungenmightbeuseful
as paleoseismic sites only if landsliding that resulted from
highgroundwatercanbeanalyticallyprecluded.However,
few studies have analytically demonstrated a seismic
origin for these features. If ridge-top grabens in seismi-
callyactiveregionsdevelopandactivatesolelyinresponse
to strong seismic ground-shaking, the in-fill deposits
would indeed provide a paleoseismic record. However,
if these features also activate by aseismic landsliding
resulting from elevated groundwater, then their use in
paleoseismic studies would be severely limited.
GEOLOGIC SETTING
The geology of the Anaheim Hills area is characterized
by a northward-dipping section of sandstone and siltstone
oftheMiocene-agePuenteFormation(Schoellhameretal.,
1981). Our field mapping of the Santiago landslide and
adjacent parts of the Anaheim Hills indicates that bedding
dips range from 78 to 258 to the north, and strikes range
from northeast to northwest (Figure 2). The Santiago
landslideapparently failedalongasurface alignedroughly
parallel or sub-parallel to bedding within the Puente
Formation.
The Santiago landslide occurred within the Soquel
Member and uppermost part of the La Vida Member of
the Puente Formation. The sandstone of the Soquel
Member consists of multiple, fining-upward sequences of
very coarse- to medium-grained sandstone that is poorly
cemented and weak; the sandstone is locally interbedded
with siltstone. The siltstone of the underlying La Vida
Member is interbedded with very thin beds of fine-
grained, ripple-laminated sandstone. These rocks were
deposited in a submarine fan environment within the
rapidly subsiding Los Angeles basin during Miocene time
(Critelli et al., 1995; Bjorklund et al., 2002).
Beginning in Pliocene time, compressional uplift of the
Santa Ana Mountains (Gath and Grant, 2003) produced
tilting of the Tertiary sedimentary section in the Anaheim
Hills area. Recent mapping of a series of fluvial terraces
directlywestoftheAnaheimHillsshowedthatupliftofthe
Figure 1. The Santiago landslide is located in the northern Santa Ana Mountains of southern California. 1 ft ¼0.3048 m.
Figure 2. Geologic map of the Santiago landslide and surrounding region. Base map shows the topography during 1993 with elevations in feet above
mean sea level. 1 ft ¼0.3048 m.
!
Johnson and Cotton
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–156
The Santiago Landslide: Implications for Paleoseismic Landslide Studies
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–15 7
Santa Ana Mountains has continued into Quaternary time
(Gath and Grant, 2002). It is hypothesized that blind thrust
faults are responsible for this active uplift, and that these
faults might produce large-magnitude earthquakes.
Strong seismic shaking in the Anaheim Hills area
results primarily from earthquakes on nearby strike-slip
and thrust faults. Major earthquakes on the Elsinore and
Whittier faults are capable of producing peak ground
accelerations in the range of 0.39 to 0.46 g in the Anaheim
Hills (Boore et al., 1997). The Elsinore fault has a
recurrence interval for large-magnitude (ground-ruptur-
ing)earthquakesofapproximately200years(Treimanand
Lundberg, 2003). The Whittier fault has a recurrence
interval of 760 (þ640,274) years (Working Group on
California Earthquake Probabilities, 1995). Earthquakes
on nearby blind thrust faults, such as the Puente Hills
blind thrust system (Shaw et al., 2002), can produce peak
ground accelerations in the range of 0.2 to 0.3 g in the
Anaheim Hills. Dolan et al. (2003) identified at least four
large-magnitude(Mw 7.2to7.5),Holoceneearthquakeson
the Puente Hills system. Because strong seismic ground
shaking likely affected the Anaheim Hills area repeatedly
during late Quaternary time, it could have contributed to
landsliding and opening of the ridge-top graben.
Mass grading of the Anaheim Hills area during the
1970s filled drainage valleys and excavated spur ridges to
developlevelbuildingpadsandroadsforresidentialdevel-
opment.ThetoeoftheSantiagolandslidelieswithinapart
ofthedevelopmentwherethetopographywashighlymod-
ified by grading. Although less-extensive grading was
completed along the northeast-trending ridgeline at the
head of the landslide, the subtlest geomorphic features
were obliterated or substantially altered.
GEOMORPHIC EVALUATION
We evaluated the pre-development geomorphology by
interpreting stereo pairs of historical aerial photographs.
Drainage development and incision followed the uplift of
the Anaheim Hills area, and several large, deep landslides
failed into the incised valleys. These landslides are
depicted on our photogeologic map (Figure 3). Over time,
erosion and drainage incision modified the morphology
of these deep landslides.
The upper part of one of these Quaternary landslides
(landslide A in Figure 3) coincides with the lower part of
the modern Santiago landslide. Drainage incision has
dissected the body of the ancient landslide and partially
obscured the morphology. However, the dissected head
scarp of the ancient landslide is still clearly evident.
Directly southeast of the head scarp of landslide A,
a well-developed graben with a prominent, northwest-
facing scarp and more-subdued, southeast-facing scarp
crosses the ridge obliquely. Between these scarps is an
elongate depression that forms the axis of the graben and
has a dark appearance on the aerial photographs. We
interpret the dark tones within the graben as evidence of
lush vegetation, perhaps grasses, that flourished in the
thick colluvium that filled the depression. This contrasts
with the sparser vegetation on the surrounding parts of
the ridge where the soil is thin.
The head of the Santiago landslide correlates closely
with the ridge-top graben that is visible in the historical
aerial photographs. Based on the map relationships with
landslide A and the ridge-top graben, we hypothesize that
the graben developed as a result of the upslope progres-
sion of landsliding during late Quaternary time.
SUBSURFACE INVESTIGATION OF THE
SANTIAGO LANDSLIDE
We conducted a subsurface investigation consisting of
downhole logging of 18 large-diameter bucket auger
borings drilled within the head, toe, and body of the
Santiago landslide and within adjacent areas off the land-
slide. The boring locations are shown in Figure 2. The
borings drilled within the body and toe of the landslide
encountered a basal rupture surface with a well-developed
gouge bounded by highly polished, striated surfaces
(Figure 4). The thickness of the basal rupture gouge in
these borings ranges from 0.1 to 3 ft (0.03 to 0.9 m).
By contrast, the borings within the ridge-top graben
encountered a basal rupture surface with less gouge
development; the thickness of the observed clay gouge
ranges from 0.1 to 1 in. (0.25 to 2.5 cm). In the ridge-top
graben area, numerous open fractures, colluvium-filled
fractures, and steeply dipping shears with normal offsets
were encountered above the basal rupture surface.
The log of boring LD-3 (Figure 5) provides a good
example of the geology exposed within borings in the
ridge-top graben area. In the upper 3 ft (0.9 m), the boring
encountered artificial fill placed during mass grading.
Belowthefillisan11ft(3.4m)thickdepositofcolluvium.
Below the colluvium, the sandstone has abundant open
fractures and colluvium-filled fractures that widen up-
ward;oneofthesefractureshasadistinctnormaloffset.At
a depth of 35 ft (10.7 m), the polished and striated basal
rupture surface of the landslide has a relatively thin, 0.1 to
1.0 in. (0.25 to 2.5 cm) thick, clay gouge.
In boring LD-2, we encountered thick colluvium
and colluvium-filled fractures up to 1.5 ft (0.5 m) wide
that extend to a depth of approximately 24 ft (7.3 m).
These fractures strike roughly parallel to the ridge-top
graben. The fractures in the ridge-top graben area
apparently filled with colluvium after earlier graben-
opening events.
RAINFALL AND GROUNDWATER
The Santiago landslide and associated ridge-top graben
failed during a period of intense rainfall during December
Johnson and Cotton
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–158
1992 and January 1993. Fifteen inches (38 cm) of rain,
102% of the 14.7-in. (37.3-cm) average annual rainfall for
Orange County, fell during those two months (Figure 6).
Rainfall during the previous year was also above average
andundoubtedlycontributedtoelevatedgroundwatercon-
ditions. Figure 6 shows the yearly rainfall record for two
nearby rainfall stations. Rainfall during the winter of
1992–1993 was exceptionally high when compared with
the rainfall record from preceding years.
Piezometer data from Eberhart and Stone (1996)
indicate that groundwater levels were elevated within
the landslide mass and surrounding area at the time of
failure (Figure 7). Subsequent installation of dewatering
wells and horizontal drains has lowered groundwater
Figure 3. A photogeologic map of ancient landslides in the vicinity of the Santiago landslide. Topographic base shows conditions before mass
grading. The elevations are in feet above mean sea level. 1 ft ¼0.3048 m.
The Santiago Landslide: Implications for Paleoseismic Landslide Studies
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–15 9
levels and substantially improved the stability of the
landslide mass (McLarty and Lancaster, 1999b). The
Santiago Landslide has not moved since completion of
the dewatering system.
Little historical data are available regarding the
groundwater conditions in the Anaheim Hills area before
development. Early geotechnical investigations did not
include installation of piezometers to evaluate the ground-
water levels. Exploratory borings drilled before develop-
mentwerefew,widelyspaced,andgenerallyshallow;most
did not encounter groundwater. However, earlier inves-
tigationsoftheSantaAnaMountainsshowedspringsinthe
area of landslide A (Schoellhamer et al., 1954). Permeable
strata that are exposed in the vicinity of the Santiago
landslide can be traced up-dip through the subsurface to
a south-facing, anti-dip slope where recharge occurs.
If landslides and associated ridge-top graben in the
Anaheim Hills area are currently being activated during
wet winters (such as 1992–1993), then it is highly likely
thattheywouldhavebeenactivatedduringtheevenwetter
periods of late Quaternary time. Several paleoclimatic
studies conducted in southern California have found evi-
dence of wet periods during late Pleistocene and Holocene
time. Templeton (1964, described in Stout, 1977) evalu-
ated the latest Pleistocene rainfall history of southern Cal-
ifornia using dendrochronologic analysis of cypress
samplesrecoveredfromtheLa Breatar pitsandconcluded
that average annual precipitation during a late Pleistocene
wet period (14.90 ka to 14.89 ka) ranged from two to five
times the current average annual rainfall for Los Angeles.
Quade et al. (2003) studied wetland deposits in southern
Nevada and found evidence for three late Pleistocene-
to-Holocenewetperiods,datedat ,26.3to16.4ka,14.5to
12.3 ka, and 11.6 to 9.5 ka, when groundwater recharge
and discharge from desert springs was high. Miller et al.
(2001) studied fan development of debris flow at Silurian
Lake in the Mojave desert and found evidence of a wet
period between 6.5 and 6.3 ka. Owen et al. (2003) dated
latero-frontalmorainesintheSanBernardinoMountainsof
southern California and found four glacial advances dated
at 20 to 18 ka, 16 to 15 ka, 13 to 12 ka, and 9 to 5 ka; the
authors further concluded that these glacial advances
occurred during periods of increased winter precipitation
and decreased summer temperatures. Clearly, the late
Quaternary climate included wet periods when ground-
water recharge rates were relatively high, increasing the
probabilityofaseismicactivationofdeep-seatedlandslides
and ridge-top grabens.
LIMIT-EQUILIBRIUM ANALYSES
Although the late Quaternary paleohydrologic and
paleoseismic conditions that resulted in the upslope
progression and graben development are not known
directly from this study, we evaluated the contribution of
both strong seismic shaking and elevated groundwater by
performing limit-equilibrium slope-stability analysis on
cross section A-A9. Specifically, we used the pre-grading
profile and modeled landslide A and the ridge-top graben
as a single block with a tension crack at the upslope end.
These analyses were performed using three different
groundwater levels (Figure 8). The highest groundwater
Figure 4. Photograph looking upward at the basal rupture surface of the Santiago landslide in boring LD-15 located within the central portion of the
landslide. Note the polished, striated, upper-bounding surface that overlies a thick, cohesive gouge.
Johnson and Cotton
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–1510
Figure 5. Log of boring LD-3 within the ridge-top graben. Note the thick accumulation of colluvium and steeply dipping, colluvium-filled fractures. 1
ft ¼0.3048 m.
The Santiago Landslide: Implications for Paleoseismic Landslide Studies
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–15 11
level corresponds to the level at the time of failure during
January 1993. The lowest groundwater level approx-
imates conditions during a dry period, when groundwater
levels were below the rupture surface of the landslide.
The third groundwater level is a hypothetical intermedi-
ate piezometric surface used to complete the analysis. To
evaluate displacement resulting from seismic ground
motion, we used a computer program by Jibson and
Jibson (2002) that incorporates the methods of both
Newmark (1965) and Bray and Rathje (1998). The
seismic-displacement input-parameters are provided on
Table 1, and the results of our analysis are shown on
Table 2.
DISCUSSION
Our subsurface observations support the hypothesis
that a well-developed, ridge-top graben is present at the
head of the Santiago landslide. The presence of a thick
accumulation of colluvium is not easily explained in a
ridge-top setting without graben development. Open and
colluvium-filled vertical fractures, as well as shears
having normal displacements, also indicate a history of
extensional deformation of the ridgeline.
A representative cross section (A-A9, Figure 7)
shows our interpretation of the subsurface relationships
between landslide A, the ridge-top graben, and the
Santiago landslide. The development of a thick, basal
rupture gouge in the body and toe of landslide A
implies that either this ancient landslide has experienced
considerably more displacement than the ridge-top
graben or that the basal rupture surface followed a weak
bed that thinned toward the ridge-top. The development
of a thick, basal rupture gouge would require repeated
displacements that would total more than the approx-
imately 1-ft (0.3-m) maximum displacement that was
recorded during the 1992–1993 event. The geomor-
phology of the ancient landslide that is visible in aerial
photographs before development also implies that
landslide A has experienced considerable, cumulative
displacement. Thus, we propose a model in which
landslide A originally failed without involving the
ridgeline and development of the graben followed as
a result of upslope progression of the landsliding. This
progression likely resulted from development of a steep
head scarp and loss of lateral support along the
ridgeline.
Our limit-equilibrium analysis confirms that at the
highest groundwater level, the landslide and graben acti-
vated, as they did during January 1993; the calculated
seismic displacements at this groundwater level are large
(3.2 m to 8.1 m). At the intermediate and low ground-
Figure 6. Rainfall records for stations located within 5 miles (8 km) of the Santiago landslide. 1 in.¼25.4 mm.
Johnson and Cotton
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–1512
water levels, our analysis shows that the landslide and
graben remain static unless triggered by seismic ground
motion. Therefore, our analysis shows that past activation
of landslide A and the associated ridge-top graben likely
occurred in response to either high groundwater or strong
seismic ground motion.
CONCLUSIONS AND IMPLICATIONS FOR
PALEOSEISMIC STUDIES
The Santiago landslide and the associated ridge-top
graben provide an example of the re-activation of a ridge-
top graben by aseismic landsliding related to elevated
groundwater conditions. Based on our limit-equilibrium
analyses, both elevated groundwater and strong seismic
shaking have likely triggered previous movement epi-
sodes of the landslide and the ridge-top graben. Colluvial
wedges preserved within the ridge-top graben and
produced by these very different triggering events would
be indistinguishable and could be misinterpreted as
representing the late Quaternary paleoseismic record.
Therefore, we conclude that ridge-top graben deposits
should be used to date paleoseismic events only if the
potential for activation by aseismic landsliding associated
Figure 7. Cross section A-A9 illustrating the subsurface relationships between the Santiago landslide and landslide A. Also note the high groundwater
levels during January 1993 when the Santiago landslide was active. 1 ft ¼0.3048 m.
Figure8.Generalized cross sectionA-A9 usedfor limit-equilibrium analyses. Thetopographicprofiledepicts conditionsbeforemassgrading.Thestatic
factors of safety (FS) for the three groundwater conditions are: 1.0 for high (H), 1.15 for intermediate (I), and 1.3 for low (L) groundwater conditions.
1ft¼0.3048 m.
The Santiago Landslide: Implications for Paleoseismic Landslide Studies
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–15 13
with intense rainfall and high-groundwater conditions can
be clearly precluded.
ACKNOWLEDGMENTS
William F. Cole, Christopher J. Sexton, Randall W.
Jibson, and an anonymous reviewer provided comments
that improved this manuscript. John Coyle, Dale Marcum,
and John Wallace assisted greatly with data collection.
Tim Sneddon assisted with limit-equilibrium analyses.
Julia Lopez and Noli Farwell drafted the figures.
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Table 1.Seismic ground motion parameters.
Fault Distance to Fault (km) Mw PGA* (g)
Elsinore 6.5 6.7 0.46
Whittier 6.6 6.8 0.39
*Boore et al. (1997).
Table 2.Seismic-displacement calculation results.
Groundwater
Level Ky
Estimated
Displacement
High 0.001 126 to 310 in.
(3.2 to 7.9 m)
1
319 in. (8.1 m)
2
Intermediate 0.03 70 to 172 in.
(1.8 to 4.4 m)
1
34 in. (0.9 m)
2
Low 0.055 43 to 138 in.
(1.1 to 3.5 m)
1
19 in. (0.5 m)
2
1Estimated displacements by method of Bray and Rathje (1998).
2Estimated displacements by method of Newark (1965).
Johnson and Cotton
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–1514
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Paleoenvironments and Paleohydrology of the Mohave and
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Boulder, CO, Special Publication 368, pp. 165–188.
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Bulletin Seismological Society America, Vol. 92, No. 8,
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Montana, USA:Geomorphology, Vol. 41, pp. 309–322.
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California:California Geology, Vol. 30, No. 5, pp. 99–105.
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creep in Olympic Mountains, Washington:Geological Society
America Bulletin,Vol. Vol. 82,, pp. 1811–1822.
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two conspicuous ridge-top scarps in southern Coast Mountains,
British Columbia:EOS, Transactions, American Geophysical
Union,Vol. 78, No. 17, suppl., pp. S316–S317.
TREIMAN,J.AND LUNDBERG, M. (compilers), 2003, Elsinore fault zone,
Glen Ivy section,in Quaternary Fault and Fold Database of the
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Topographic and Structural Conditions in Areas of Gravitational
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of October 2, 1915, in Pleasant Valley, Nevada, and Some
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1994 to 2024:Bulletin Seismological Society America, Vol. 85,
No. 2, pp. 379–439.
The Santiago Landslide: Implications for Paleoseismic Landslide Studies
Environmental & Engineering Geoscience, Vol. XI, No. 1, February 2005, pp. 5–15 15
July 5, 2023
Project No. TET 22–236E
Geotechnical Engineering ● Engineering Geology
GEOTECHNICAL EVALUATION
AND GROUNDWATER IMPACT ASSESSMENT
SANTIAGO LANDSLIDE
ANAHEIM HILLS
Anaheim, California
Prepared for: City of Anaheim, Department of Public Works
200 S. Anaheim Boulevard, Suite 276
Anaheim, California 92805
Prepared by: Tetra Tech
21700 Copley Drive, Suite #200
Diamond Bar, California 91765
21700 Copley Drive, Suite #200 * Diamond Bar, CA 91765 * Tel: 909-860-7777
Project No. TET 22-236E
July 5, 2023
Mr. Rudy Emami
Director of Public Works
City of Anaheim, Department of Public Works
200 S. Anaheim Boulevard, Suite 276
Anaheim, California 92805
Subject: GEOTECHNICAL EVALUATION AND GROUNDWATER IMPACT ASSESSMENT
SANTIAGO LANDSLIDE
Anaheim Hills
City of Anaheim, California
Dear Mr. Emami:
Tetra Tech is pleased to submit this report that presents the results of our geotechnical evaluation and
groundwater impact assessment for the Santiago Landslide of Anaheim Hills, in the City of Anaheim,
California. This study relied primarily on readily available past geotechnical and groundwater
monitoring data by others as well as new data from existing groundwater monitoring wells and
inclinometers installed during 1992/1993 Santiago Landslide emergency response efforts. From our
review, geologic, engineering and hydrogeologic analyses were performed to evaluate the effects of
groundwater on the stability of the landslide within the Santiago Geologic Hazard Abatement District
(SGHAD). Results of analyses were then used to assess the impacts of the recent 2022/2023 rainfall
season, as well as the potential for renewed landslide movement if the current dewatering operations
are terminated.
This report includes a brief summary of the history of the events that took place during the 1992/1993
Santiago Landslide emergency response efforts, the establishment of the SGHAD, and implementation
of the Plan of Control adopted by the SGHAD. This report also includes our monitoring efforts,
engineering, geologic and hydrogeologic analyses, and includes a summary of our findings,
conclusions, and recommendations. The accompanying plates and appendices include compilations of
collected data, geologic and hydrogeologic maps and exhibits, and graphical output of our analyses.
We appreciate the opportunity to provide our professional services on this project. If you have any
questions regarding this report or if we can be of further service, please do not hesitate to contact the
undersigned.
Respectfully submitted,
Tetra Tech BAS, Inc.
Patrick M. Keefe, CEG
Supervising Engineering Geologist
Peter Skopek, PhD, GE
Principal
Distribution: Addressee (pdf by email REmami@anaheim.net)
Mr. Carlos Castellanos (pdf by email CCastellanos@anaheim.net)
Filename: 2023-07-05 SGHAD Geotechnical Evaluation and Groundwater Impact RPT .docx
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
i
TABLE OF CONTENTS
Page
1. INTRODUCTION AND PURPOSE ................................................................................... 1
2. THE SANTIAGO LANDSLIDE ......................................................................................... 2
3. GEOLOGIC HAZARD ABATEMENT DISTRICT AND PLAN OF COTNROL ............ 4
3.1. HISTORY OF SGHAD GROUNDWATER EXTRACTION ...................................... 6
3.1.1. VERTICAL DEWATERING WELLS .............................................................................. 6
3.1.2. HORIZONTAL DRAINS .............................................................................................. 7
3.2. HISTORY OF SGHAD GROUNDWATER MONITORING ...................................... 8
3.3. HISTORY OF SGHAD INCLINOMETER MONITORING ..................................... 10
4. GEOLOGIC AND HYDROGEOLOGIC SETTING ........................................................ 12
4.1. LOCAL GEOLOGY ................................................................................................... 12
4.2. GROUNDWATER ..................................................................................................... 12
4.3. WATERSHED BOUNDARY .................................................................................... 13
4.4. GROUNDWATER RECHARGE............................................................................... 15
4.4.1. RAINFALL .............................................................................................................. 15
4.4.2. IRRIGATION ............................................................................................................ 16
4.4.3. EVAPOTRANSPIRATION .......................................................................................... 16
4.4.4. INFILTRATION AND HYDRAULIC CONDUCTIVITY ................................................... 17
4.5. GROUNDWATER DISCHARGE ............................................................................. 17
5. CURRENT MONITORING BY TETRA TECH .............................................................. 19
5.1. OBSERVATION WELLS AND STANDPIPE PIEZOMETERS .............................. 19
5.2. INCLINOMETERS .................................................................................................... 19
6. HYDROGEOLOGIC AND ENGINEERING ANALYSES ............................................. 20
6.1. GROUNDWATER FLOW AND GROUNDWATER MONITORING ..................... 20
6.2. GROUNDWATER LEVELS ..................................................................................... 20
6.3. SLOPE STABILITY................................................................................................... 21
6.4. GROUNDWATER LEVEL EFFECT ON STABILITY ............................................ 22
6.5. POTENTIAL EFFECT OF DEWATERING SHUT-OFF .......................................... 24
7. CONCLUSIONS AND RECOMMENDATIONS ............................................................ 26
7.1. SGHAD FUNDING AND PROJECTED REVENUE RESOURCES ........................ 26
7.2. IMMINENT THREAT OF LANDSLIDE REACTIVATION.................................... 26
7.3. SENSITIVITY OF GROUNDWATER CONTRIBUTIONS ..................................... 26
7.4. WATER CONSUMPTION ANALYSIS BY ANAHEIM PUBLIC UTILITIES ....... 26
7.5. OUTDOOR WATER RESTRICTIONS ..................................................................... 27
8. LIMITATIONS .................................................................................................................. 29
9. SELECTED REFERENCES ............................................................................................. 30
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
ii
FIGURES, PLATES & APPENDICES
FIGURES
Figure 1 – Approximate Boundaries of Santiago Landslide
Figure 2 – SGHAD Boundaries
Figure 3 – Generalized Aquifer Conditions
Figure 4 – SGHAD Watershed Contribution Limits
Figure 5 – Annual Rainfall Records Over Past 30 years for Anaheim Hills
PLATES
Plate 1 – SGHAD Facilities Location Plan
Plate 2 – Geologic Map
Plate 3 – Geologic Cross-Sections 1 – 1’ through 4 – 4’
Plate 4 – Groundwater Profiles Through the Landslide Mass
APPENDICES
Appendix A – Cumulative and Incremental Inclinometer Surveys Plots for SI-4
Appendix B – Groundwater Elevation Plots with Monthly Precipitation
Appendix C – Graphic Relationships of Various Groundwater Surfaces (Plates C-1 through C-4)
Appendix D – Slope Stability Analyses
Appendix E – Water Consumption Analysis for the Santiago Geological Hazard Abatement
District (Anaheim Public Utilities Department, dated June 29, 2023)
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
1
1. INTRODUCTION AND PURPOSE
Due to the heavy rainfall that occurred during January through March of 2023 (17.5 inches), the
City of Anaheim contracted with Tetra Tech to assess geotechnical conditions within the Santiago
Geologic Hazard Abatement District (SGHAD). Our services included a detailed assessment of
readily available past geotechnical and groundwater monitoring data by others and collection of
new groundwater and inclinometer data from the existing monitoring devices. With this data,
geologic, engineering, and hydrogeologic analyses were performed to evaluate the impacts of the
recent 2022/2023 rainfall as well as the potential for renewed landslide movement if the current
dewatering operations are terminated.
This report includes a brief summary of the history of events that took place during the 1992/1993
Santiago Landslide emergency response efforts, the establishment of the SGHAD, and
implementation of the Plan of Control (POC) adopted by the SGHAD. This report also
summarizes our monitoring efforts, engineering, geologic and hydrogeologic analyses, and
includes a summary of our findings, conclusions and recommendations. The attached plates and
appendices include compilations of collected data, geologic and hydrogeologic maps and exhibits,
and graphical output of our analyses.
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
2
2. THE SANTIAGO LANDSLIDE
The Santiago Landslide is a dormant landslide that encompasses roughly 25 acres in the Anaheim
Hills area of Anaheim, California. The Santiago Landslide is one of the largest landslides to affect
urban public property within Orange County. The landslide mass encroaches within 60 residential
properties and public and private streets. The limits of the landslide were defined at the ground
surface (now obscured) as a discontinuous zone of extensional ground cracks along the head scarp
of an upslope-bounding ridgeline and local compressional ground deformation (bulges) along the
poorly developed landslide toe. The basal slip surface of the landslide has been interpreted to
reach maximum depths on the order of 200 feet (Eberhart & Stone, Inc, 1996).
Initial movement of the landslide was recognized as relatively small cracks in road surfaces during
the summer months of 1992. Movement of the landslide mass accelerated in January 1993
following intense rainfall in December 1992 and January 1993. This episode of ground movement
resulted in development of more open ground cracks, damage to multiple underground utility lines,
damage to swimming pools and private residences, and deformation and development of ground
cracks within several public and private streets (E&S, 1996). By mid-February 1993, extensive
dewatering efforts coordinated by the City’s geotechnical consultant, Eberhart & Stone, Inc.,
(E&S) successfully arrested further landslide movement. The approximate limits of the Santiago
Landslide are shown in Figure 1.
Figure 1. Approximate Boundaries of Santiago Landslide
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
3
The primary factors that have been attributed to the 1992/1993 landslide mobilization include:
• North-facing hillside terrain in conjunction with unfavorably north-dipping geologic
structure and south-dipping ancient faults.
• Pre-existing planes of weakness within the underlying bedrock.
• Elevated groundwater.
In essence, the landslide was triggered by buoyancy forces due to a rise in groundwater that
reduced the shear strength of the already relatively weak bedrock that resulted in the landslide
movement in a downslope direction along the unfavorably dipping bedrock bedding.
Due the lateral extent and depth of the landslide, combined with its location within a moderately
to heavily developed urban environment, conventional stabilization repair methods such as earth
buttressing, engineered tiebacks, or other permanent mechanical ground stabilization methods
were deemed impracticable and even unfeasible. Therefore, continuous groundwater dewatering
to reduce the pore pressures and associated monitoring programs were implemented to manage the
groundwater conditions and stabilize the landslide. Whereas this method of mitigation is common
and effective, it did not stabilize the landslide with a sufficient margin of safety that would forgo
requirements for permanent maintenance and monitoring. This approach was deemed acceptable
because an important benefit of this stabilization method is that it can always be scaled up to
increase the amount of dewatering in case the monitoring indicates unfavorable increase in
groundwater levels.
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
4
3. GEOLOGIC HAZARD ABATEMENT DISTRICT AND PLAN OF COTNROL
The Anaheim City Council formed the SGHAD on March 16, 1999 under the authority of the
California Public Resources Code, Division 17, Section 26500 et seq. with the approval of City of
Anaheim Resolution 99R-50. Anaheim and the SGHAD ultimately entered in an agreement on
June 10, 1999 that required the City of Anaheim to:
a) transfer and assign all rights and interests that it held in specified Dewatering Facilities,
b) provide the SGHAD access to such Dewatering Facilities, and
c) transfer $3.5 million to the SGHAD for the purpose of construction, acquisition, operation,
maintenance, and repair of Dewatering Facilities and for the purpose of monitoring, abating
and/or stabilizing the Santiago Landslide.
The SGHAD’s obligation under the Agreement was to assume sole and total responsibility for all
ownership, control, operational, maintenance, and repair responsibilities relating to the Dewatering
Facilities. Specifically, the agreement requires the SGHAD to operate, maintain, and repair all or
part of the Dewatering Facilities, as well as any additional new or replacement facilities that may
be constructed or installed in a manner within its discretion which will control groundwater levels
to prevent reactivation and/or to abate movement of the Santiago Landslide (Benink, 2021).
As part of the agreement, a “Plan of Control” (POC) was established to allow the SGHAD to
permanently monitor and maintain the Santiago Landslide. The primary objective of the POC is
to achieve groundwater elevations within the SGHAD no higher than those recorded on October
5, 1994 each and every year at the onset (October 15) of the annual rainy season. Annual reporting
requirements of the POC include documenting the inspection and monitoring results for the
preceding rain year by November 1 of each year and addressing both the mechanical state of the
dewatering system and evaluate preparedness for the up-coming rainfall year, particularly
groundwater elevations compared to the October 5, 1994 maximums (POC, 1999).
The POC includes provisions for retention of a “Primary Geologic/Geotechnical Consultant”, a
“Pump/Well Contractor” and a “Review Geologic/ Geotechnical Consultant” to provide required
technical expertise and recommendations to the SGHAD Board.
1) The role of the Primary Geologic/Geotechnical Consultant (currently ENGEO) is to:
conduct groundwater monitoring in monitoring wells and piezometers,
perform inclinometer surveys once per year,
compile pump discharge volumes and report and analyze findings.
2) The role of the Pump/Well Contractor (currently Charles King Company) is to:
service pumps,
monitor performance and,
report to the Primary Consultant.
3) The role of the Review Geologic/Geotechnical Consultant (currently ENGEO) is to assist
the SGHAD Board in reviewing reports and activities of the Primary Consultant and
Pump/Well Contractor.
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
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According to the POC, “It has been determined from hydrogeologic analyses that the rising
groundwater in the Santiago landslide area was primarily due to local recharge of applied
landscape irrigation. Therefore, properties contributing to the destabilizing elevated groundwater
include those that are contiguous with and tributary to properties directly underlain or damaged
by Santiago Landslide movements of 1992-93. These “tributary” properties influenced original
destabilization of the Santiago Landslide by groundwater recharge and their on-going recharge
water must be withdrawn by the GHAD dewatering system. Therefore, these “tributary”
properties should be included in the GHAD, along with the properties within the surface distress
boundary.” Properties included within the SGHAD encompass an area of approximately
152 acres that includes 305 residential properties with public and private streets as shown in
Figure 2.
Figure 2. SGHAD Boundaries
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
6
3.1. HISTORY OF SGHAD GROUNDWATER EXTRACTION
3.1.1. Vertical Dewatering Wells
Based on our review of available data, a total of 39 vertical dewatering wells (DW) were installed
during the emergency response efforts of 1993. Dewatering well DW-38 was drilled by others for
the purpose of attaining Conditions of Approval for the Point Premier residential development that
was constructed at the western terminus of Avenida de Santiago, well after the 1993 emergency
operations. Dewatering well DW-40 was reportedly never drilled (Amec 2018).
Metered discharge volumes and the pumping water level are recorded at each of the dewatering
wells on an approximately monthly basis by the Charles King Company (CKC). CKC’s logs also
include notes regarding any required equipment replacements or other maintenance that is
performed. Table 1 presents and inventory of each dewatering well with notes as reported by
ENGEO (2023).
Table 1
Inventory of Dewatering Wells
Well
No.
Drilled
Depth (ft) Notes
DW-1 55 No records. Not included in the active dewatering system, per the 1999 POC
DW-2 50
Currently operational DW-3 52
DW-4 50
DW-5 50
DW-6 49 DW-6 was abandoned and replaced by DW-41
DW-7 50.5
Currently operational DW-8 50
DW-9 49
DW-10 132 DW-10 was abandoned and replaced by DW-39
DW-11 50 No records. Not included in the active dewatering system, per the 1999 POC
DW-12 unknown Currently operational
DW-13 40 No records. Not included in the active dewatering system, per the 1999 POC
DW-14 90
Currently operational
DW-15 90
DW-16 75
DW-17 89
DW-18 57.5
DW-19 52
DW-20 90
DW-21 50 No records. Not included in the active dewatering system, per the 1999 POC
DW-22 89 Currently operational
DW-23 unknown Non-operational. Requires maintenance due to blockage in discharge pipes
DW-24 unknown No records. Not included in the active dewatering system, per the 1999 POC
DW-25 unknown Non-operational. Requires maintenance due to blockage in discharge pipes
DW-26 94.5 Currently operational
DW-27 100 No records. Not included in the active dewatering system, per the 1999 POC
DW-28 300
Currently operational
DW-29 200
DW-30 300
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
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DW-31 200
Currently operational
DW-32 300
DW-33 200
DW-34 200
DW-35 200
DW-36 330
DW-37 290
DW-38 unknown Drilled by others, no pump installed. Not included in the active dewatering
system
DW-39 360 Currently operational
DW-40 N/A Not drilled
DW-41 360 Currently operational
As reported by ENGEO, the approximate annual pump rates for all operating dewatering wells
over the last 7-year period are presented in Table 2 below:
Table 2
Dewatering System Pump Rates
Calendar Year
Approximate Annual
Dewatering System Yield
(gallons/yr)
2022 14,928,500
2021 12,979,700
2020 13,578,000
2019 13,615,200
2018 13,305,200
2017 12,734,800
2016 11,764,500
3.1.2. Horizontal Drains
A total of 87 horizontal drains were constructed in association with the Santiago Landslide
emergency response efforts of 1993. The horizontal drains consist of small diameter boreholes
(typically 2 to 3 inches) that were drilled into the face of a slope at a slight upward angle to allow
gravity flow and discharge of groundwater. Slotted PVC casing/pipe was then inserted into the
hole to collect any groundwater that enters the hole and to transmit the collected water out to the
slope face. The outer 5 to 10 feet of the casing was typically solid to allow a seal to be placed
around the pipe at the slope face to force the groundwater flow into the pipe and discharge to a
collection gallery at the slope face (AMEC, 2017).
At the time of the initial emergency response efforts, essentially all of the horizontal drains were
reportedly flowing after they were installed. About a month after the January 20, 1993 landslide
movement, the estimated volume of discharge from the horizontal dewatering system far exceeded
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
8
the pumping discharge from the vertical dewatering wells for several weeks and peaked at an
average of 170,000 gallons per day in late February – early March 1993 (Wood, 2018).
Over time, the outflow from the horizontal drains diminished steadily to the point where most
drains no longer continued to flow except during periods of high rainfall. By October of 2005,
flow was observed and measured in 9 of the drain outlets, and then diminished to flow from only
5 of the 37 horizontal drains in June 2006 (Wood, 2018). Based on ENGEO’s 2022 Annual
Monitoring report, only 3 of the 87 horizontal drains were flowing at the time of their last site visit.
The combined approximate outflow total from the 3 flowing drains was measured to be about
1,490 gallons per day in May of 2022.
The approximate location of all the horizontal drains installed within the SGHAD are shown on
the SGHAD Facilities Location Plan – Plate 1.
3.2. HISTORY OF SGHAD GROUNDWATER MONITORING
A total of 37 observation wells and 5 nested standpipe piezometers were installed to form the
monitoring system. The observation wells (P-wells) typically consist of small diameter (2 to
4-inches) slotted PVC pipe that was inserted into a drilled borehole. Observation wells P-1 through
P-28 are reportedly composed of slotted PVC pipe with an end cap installed to the full depth of
each borehole (E&S, 1996). The annular space around the PVC pipe was backfilled with No.4
sand to allow free flow of groundwater into the pipe. Upon completion of each well, the casing
was capped with a flush-mount well box embedded in concrete to provide a nominal seal at the
top of the well. Observation wells P-22 B, P-22C, P-25B, P-25C, P-26B, P-26C, PA, PT-A, and
PT-B were apparently drilled by others after the emergence response efforts. No details regarding
slotted pipe and annular space backfill for these wells were available for review during this study.
The standpipe piezometers (PZ-wells) are comprised of “nested” piezometers intended to provide
information on possible differences in water pressure that may be present at various depths in the
strata that comprise the underlying bedrock. The nested piezometers have slotted casing installed
only in a specific interval within a borehole with bentonitic seals above and below to isolate that
specific interval. Each of the PZ-1 through PZ-5 installations include two standpipes and the letter
designations represent slotted monitoring intervals that are separated by bentonite seals.
The approximate location of each observation well and standpipe piezometer is indicated on the
attached SGHAD Facilities Location Plan – Plate 1. Details of each monitoring well are presented
in Table 3.
Initially, annual monitoring reports were prepared by AMEC Earth & Environmental (AMEC) and
their predecessor companies, followed more recently by ENGEO. The last formal annual
monitoring report prepared by ENGEO was dated October 31, 2022 and summarized recorded
groundwater depths acquired on December 21, 2021. More current groundwater depths were
collected by ENGEO on January 31, 2023 but were not included in a formal monitoring report.
Raw groundwater data from the January 2023 recording date was presented to Tetra Tech in an
Excel spreadsheet for use in this report.
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Table 3
Inventory of Groundwater Observation Wells & Standpipe Piezometers
Well
No.
Drilled
Depth (ft) Well Notes
P-1 100
Screened total depth per E&S
P-2 100
P-3 100
P-4 100
P-5 60
P-6 60
P-7 80
P-8 70
P-9 70
P-10 70
P-11 100
P-12 101
P-13 100
P-14 50
P-15 100
P-16 50
P-17 60
P-18 50
P-19 100
P-20 104
P-21 101
P-22 100
P-22B Unknown Unknown installation details P-22C Unknown
P-23 200
Screened total depth by E&S P-24 190
P-25 200
P-25B Unknown Unknown installation details P-25C Unknown
P-26 200 Screened total depth by E&S
P-26B Unknown Unknown installation details P-26C Unknown
P-27 260 Screened total depth by E&S P-28 200
PZ-1C 200 Screened interval: 138’-143’ by E&S
PZ-1D 200 Screened interval: 183’-188’ by E&S
PZ-2A 195 Screened interval: 86.5’-91.5’ by E&S
PZ-2C 195 Screened interval: 182’-197’ by E&S
PZ-3B 236 Screened interval: 126’-131’ by E&S
PZ-3C 236 Screened interval: 201’-206’ by E&S
PZ-4B 204 Screened interval: 108’-113’ by E&S
PZ-4C 204 Screened interval: 161’-166’ by E&S
PZ-5B 214 Screened interval: 95’-100’ by E&S
PZ-5C 214 Screened interval: 193’-198’ by E&S
PA Unknown
Unknown installation details PT-A Unknown
PT-B Unknown
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3.3. HISTORY OF SGHAD INCLINOMETER MONITORING
A total of 10 inclinometers (SI’s) that varied in depth from 180 feet to 260 feet were installed by
E&S during the Santiago Landslide emergency response efforts of 1993. The approximate
location of each inclinometer is indicated on the attached SGHAD Facilities Location Plan –
Plate 1. The inclinometers typically consist of thick-walled PVC casing that is inserted and
grouted in place in a drilled borehole. The inside of the casing includes longitudinal slots in the 4
quadrants of the casing. An inclinometer probe with guide wheels that fit in the slots is lowered
into the casing and precise measurements of the pipe inclination are measured at 2-foot intervals
along the depth of the casing. A baseline set of measurements is compared to subsequent sets of
measurements, and any displacement of the casing can be interpreted from the change in casing
inclination. Inclinometers can typically detect displacements as small as about 0.01 inches.
From February of 1993 through March of 2000 the inclinometers were monitored by E&S. The
results of these monitoring efforts indicated that very small offsets had occurred in inclinometers
SI-4, SI-5 and SI- 9. No discernable offsets were reported within the remaining inclinometers.
After March of 2000 E&S purchased a new inclinometer probe, field data collector, and computer
software package for data evaluation. As reported by Wood (name successor of AMEC), their
review of the E&S annual reports from 2000 through 2003 indicated the following:
• Only 9 of the inclinometer casings were monitored as the damage that occurred to the SI-7
during its installation apparently made monitoring unreliable with the possibility that the
probe might become lodged in the casing.
• Data from inclinometers SI-4, SI-5 and SI-9 were evaluated to determine if any significant
additional movements had occurred. The data from the remaining casings would be evaluated
only if significant movements were recognized in SI-4, SI-5 and SI-9.
• Additional small incremental movements that decreased in magnitude through time were
reported in inclinometers SI-5 and SI-9 through 2002.
• By the end of the 2002-2003 monitoring year the magnitude of ground movements observed
in SI-4, SI-5 and SI-9 appear to have subsided to levels below the ability of the of the
instrumentation to reliably detect movement.
The existing inclinometers, with the exception of SI-7, were re-surveyed by Wood in July of 2004
to establish a new baseline for comparison with future surveys. Wood then performed annual
monitoring of the each of the 9 inclinometers between 2004 and July 2008. Comparison of the
2005, 2006, 2007 and 2008 surveys with the 2004 baseline data indicated that no significant
landslide movement had occurred over that time period. Following the 2008 measurements, Wood
recommended that annual inclinometer monitoring be discontinued until a substantial rise in the
groundwater levels was observed.
In 2012, Wood recommended that annual inclinometer measurements be performed at SI-4, which
was considered to be the most sensitive installation with regard to detecting possible future
landslide movement. The final set of measurements by Wood was collected on December 18,
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2017 and review of the processed results showed no evidence considered indicative of landslide
movement. Cumulative and incremental plots of Wood’s inclinometer surveys for SI-4 are
included in Appendix A.
In 2019, ENGEO replaced Wood as SGHAD Primary Geologic/Geotechnical consultant. In
March 2019, ENGEO established new baseline readings for SI-2, SI-3, SI-4, SI-6, SI-8, SI-9, and
SI-10 and followed by a second monitoring event in November and December 2019. Inclinometers
SI-1 and SI-7 were reported damaged and no longer capable of monitoring. Based on the
March 2019 survey (final inclinometer survey by ENGEO), no significant displacement indicative
of soil movement was identified by ENGEO. No inclinometer plots were presented by ENGEO.
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4. GEOLOGIC AND HYDROGEOLOGIC SETTING
4.1. LOCAL GEOLOGY
The Santiago Landslide is located in the Anaheim Hills area of the northern Santa Ana Mountains.
The northern Santa Ana Mountains are a dominate feature in the northern Peninsular Ranges of
coastal southern California and form the southeast margin of the Los Angeles basin. The
mountains expose the most complete section of the late Mesozoic and Cenozoic sequence that
underlies the north part of the Peninsular Ranges physiographic province (Schoellhamer
et al., 1981).
The Santiago Landslide, as mapped by various consultants, is largely underlain by northward-
dipping sequences of sandstone and siltstone assigned to the Soquel Member and the underlying
La Vida Member of the Upper Miocene-age Puente Formation. These rocks were deposited in a
marine environment within the rapidly subsiding Los Angeles basin during Miocene time. Other
bedrock units beneath the landslide area include basaltic volcanic rock assigned to the middle
Miocene El Modeno Volcanics and sandstone and conglomerates assigned to the middle Miocene
Topanga Formation. Surficial units that generally mantle the bedrock include topsoil/colluvium,
alluvium and artificial fills associated with various residential developments in the area.
The Santiago Landslide occurred within the Soquel Member and uppermost part of the La Vida
Member of the Puente Formation. The Soquel Member consists primarily of sequences sandstone
that are poorly cemented and weak and is locally interbedded with siltstone. The La Vida Member
consists of siltstone that is interbedded with very thin beds of fine-grained sandstone. The
landslide failure has been interpreted to have failed along weak sandstone and siltstone bedding
planes in the bedrock units. Several bedrock faults are also believed to have formed the boundaries
of the landslide, as well as may significantly control vertical and horizontal migration of
groundwater beneath the slide mass.
The limits of the Santiago Landslide and the distribution of the major geologic units and faults in
the area, based on mapping by E&S (1996), are shown the attached Geologic Map – Plate 2.
Geologic Cross-Sections 1 -1’ though 4 – 4’, as presented within the E&S 1998 report, are
presented on the attached Geologic Cross-Sections – Plate 3.
4.2. GROUNDWATER
The groundwater regime beneath the SGHAD is complex and occurs as both unconfined and
confined aquifer conditions that are locally interconnected by fractures. The concept of confined
and unconfined aquifer conditions is shown on Figure 3. The groundwater conditions beneath the
SGHAD are largely controlled by bedrock stratigraphy, geologic structure (i.e., bedding and
faulting), hydrogeologic characteristics of the geologic unit, and sources of water.
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Figure 3. Generalized Aquifer Conditions
(From: National Groundwater Association, 2007)
Evidence of high groundwater and running springs at the ground surface has been well documented
within the Anaheim Hills areas by various sources long before significant urbanization of the area
in the late 1960’s and early 1970’s (E&S, 1996). As urbanization of Anaheim Hills progressed to
its current state, the surface water infiltration increased dramatically in response to increased
landscape irrigation. The resulting surface water contributions combined with the complex
geologic environment created the framework for historic high groundwater levels beneath the
SGHAD prior to installation of the current dewatering system.
4.3. WATERSHED BOUNDARY
The watershed contribution limits are defined for this study as the land area that channels rainfall
and irrigation water from higher to lower elevations that eventually flows inside the SGHAD
limits. The watershed limits shown in Figure 4 are formed by high points such as prominent hills
or ridges.
The SGHAD watershed area shown in Figure 4 is roughly 211.4 acres. This area is approximately
60 acres larger than the SGHAD. Of the watershed total area, approximately 85.1 acres is open
space natural slopes, approximately 57 acres are irrigated slopes and yards, and approximately
69.2 acres are impervious improvements that include residential structures, streets, and sidewalks
that typically control water runoff to storm drains.
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Figure 4. SGHAD Watershed Contribution Limits
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4.4. GROUNDWATER RECHARGE
Infiltration of surface water and subsurface inflow are the primary sources of recharge to the
groundwater system within the SGHAD limits. Subsurface groundwater flow beneath much of
the watershed boundary defined by this study and entirely beneath the SGHAD is directed to the
north and northeast (E&S, 1986). The volume of groundwater recharge is difficult to quantify
short of completing a very complex and rigorous water budget. However, based on our review of
roughly 30 years of monitoring data collected during the emergency response operations and
subsequent SGHAD reporting, we concur with various other consultant’s that groundwater
recharge is markedly influenced by seasonal rainfall and year-long irrigation.
4.4.1. Rainfall
Annual rainfall records over the past 30 years for the Anaheim Hills area are presented in Figure 5.
From the data presented, the annual totals have averaged about 14.5 inches. However, episodic
weather systems have produced annual rainfall variations ranging from as low as 2.8 inches to as
much as 32.8 inches. Though annual precipitation totals are unpredictable, historical rainfall
records can provide a reasonable median and extreme rainfall total that can be considered when
evaluating recharge potential from rainfall. It is noted that within Southern California
approximately 92% of seasonal rainfall events occur between the months of November and April.
Note: Rainfall totals shown for 2022-2023 do not extend beyond May 2023.
Sources: AMEC 2017 Annual Report Table V "Summary of Estimated Annual Rainfall Totals 1895 to 2017"
County of Orange Water Data Portal (hydstraocpublicworks.com/web.htm)
Anaheim, CA Precipitation/Rainfall Data (rainharvestcalculator.com/Rainfall/CA/Anaheim/92806)
Figure 5. Annual rainfall records over the past 30 years for Anaheim Hills
0
5
10
15
20
25
30
35
Rainfall (Inches)July through June Yearly Rainfall -1992 to 2023
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4.4.2. Irrigation
Groundwater contributions due to irrigation are affected by individual homeowners or tenants,
board members comprising a homeowner’s associations (HOA’s), and departments at the
municipal level. For example, the extent or type of landscaping for individual properties,
community common space, or public right-of-ways often varies from extremes that can be
described as “sparse desert landscape” to “tropical oasis”. Depending on the landscape practices
made by individuals, the amount of water, type of irrigation equipment, method of irrigation,
duration of irrigation, and when not to irrigate varies dramatically. Other factors, such as location
and size of property can also influence decisions regarding landscaping and irrigation practices.
If we assume the typical homeowner irrigates their lawn and garden for 15 to 20 minutes 3 times
per week, approximately 1 inch of water will have been applied to the lawn and garden space in
1 week, or 4 inches of water over the month. Assuming a modest decrease in irrigation during the
rainy season, the annual irrigation by a typical homeowner would be roughly 46 inches each year.
According to the 1996 E&S report, residential irrigation for moderate to densely landscaped
properties can be equated to roughly 50 inches to 140 inches of rainfall each year which is 3.5 to
10 times the average annual rainfall.
When comparing recharge potential from rainfall and irrigation, an overriding factor to consider
is that irrigation is typically applied at lower rates to limit runoff and enhance infiltration,
particularly on sloping terrain. Precipitation, on the other hand, is often characterized by periods
of high intensity rainfall that often results in more runoff than recharge.
To further exemplify the impacts of irrigation to groundwater recharge, E&S (1996) report
discusses January of 1995 when groundwater levels are reported to had risen in response to heavy
rains during the 1994/1995 rainy season. However, the groundwater levels continued to rise
through the 1995 dry summer months which could be explained only by the effects of irrigation.
4.4.3. Evapotranspiration
A natural process that can offset the impacts of surface water recharge, no matter what the source,
is referred to as evapotranspiration. In simple terms, evapotranspiration is the combined process
of water surface evaporation, soil moisture evaporation, and plant transpiration. Depending on
several factors that include, but are not limited to, climate, soil type, and amount of vegetation to
name a few, the rate of evapotranspiration in the Orange County region can vary from roughly 2 to
as much as 6.5 inches/month, or up to 46 inches per year (California Water Resources, 2012).
Ideally, to optimize water management and limit ground saturation and groundwater recharge due
to landscape irrigation, the rate of irrigation should be roughly equivalent to the rate of
evapotranspiration. However, in many Southern California neighborhoods, the rate of landscape
irrigation often considerably outweighs the rate of natural evapotranspiration. For example, the
Santiago Landslide initially mobilized in the summer of 1992 following several drought years that
were recorded prior to landslide mobilization (E&S, 1996). Though landslide movement was
clearly intensified by the 1992/1993 winter rainy season, landscape irrigation is believed to have
been the primary contributor to the rise in groundwater that triggered the 1992-1993 Santiago
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Landslide event. As summarized earlier in Section 3 of this report “…the rising groundwater in
the Santiago landslide area was primarily due to local recharge of applied landscape irrigation
(POC, 1999)”.
4.4.4. Infiltration and Hydraulic Conductivity
Water applied to the pervious ground surface through rainfall and irrigation enters the subsurface
through the process of infiltration. Surface water infiltration is controlled by the rate and duration
of water application, physical properties of the earth material, slope gradient, vegetation, and
surface roughness. Generally, if the supply of water is greater than the soil’s ability to infiltrate,
excess water will either accumulate on the ground surface or become runoff. On the other hand,
if water is applied at lower rates, runoff is considerably reduced, and infiltration is significantly
enhanced.
For saturated flow, i.e., flow that occurs when all pore spaces of the earth materials are completely
filled with water, hydraulic conductivity can be readily quantified through laboratory and/or in-situ
field testing. For example, the compacted soil that comprises fill materials beneath the SGHAD
typically possess hydraulic conductivity in the range of 10-6 cm/sec which can be correlated to an
infiltration rate of approximately 12 inches/year. Similarly, the hydraulic conductivity of the
bedrock materials beneath the SGHAD have been reported to possess values ranging from 10-5 to
10-6 cm/sec and thus can produce recharge rates on the order of 12 to 120 inches/year.
To put this information into perspective and to assess the potential impacts of irrigation and rainfall
on groundwater recharge potential, we can assume a hydraulic conductivity of 60 inches/year, with
14 inches/year due to rainfall and 46 inches/year due to irrigation. Based on a Google Earth
assessment, the irrigated lawns and decorative landscape areas within SGHAD range from roughly
2,000 sqft to 9,000 sqft, thus, the average recharge potential for each irrigated residential property
(avg. 5,000 sqft) can be roughly estimated at 515 gallons per day. At 305 residences within the
SGHAD, the total recharge potential is roughly 157,000 gallons per day or 38 million gallons
annually, assuming only 8 months of irrigation during the year. If we account for an annual
evapotranspiration rate of 46 inches/year, the recharge potential could be adjusted to about
9 million gallons annually. Certainly, if we consider higher recharge rates, the HOA slopes within
the SGHAD, and other residential properties not included within the SGHAD but within the
watershed contribution area shown on Figure 4, the potential recharge volume increases
substantially. Conversely, other factors such as decreasing permeability through the unsaturated
vadose zone could limit recharge potential. While the values presented above are based on rough
estimates and simplified assumptions, they are clearly reflective of the large recharge potential due
to irrigation and rainfall.
4.5. GROUNDWATER DISCHARGE
Groundwater discharge can be primarily attributed to evapotranspiration, seepage from natural
springs, subsurface outflow, and mechanical dewatering methods. Based on the history of
groundwater extraction summarized in Section 3 of this report, discharge from dewatering wells
appears to dominate the discharge regime within the boundaries of the SGHAD and was
determined to be responsible for ceasing ground movement during the 1993 landslide event.
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Groundwater discharge rates from dewatering operations within the limits of the SGHAD have
been credited with discharging upwards of 11 to nearly 15 million gallons of groundwater each
year over the last decade.
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5. CURRENT MONITORING BY TETRA TECH
Due to the amount of rainfall that occurred during January through March of 2023 (cumulative
total of 17.5 inches), the City of Anaheim contracted with Tetra Tech to provide geotechnical
consulting services to assess groundwater conditions and monitor inclinometers within the
SGHAD.
5.1. OBSERVATION WELLS AND STANDPIPE PIEZOMETERS
Tetra Tech initiated monthly groundwater monitoring beginning in April 2023. Groundwater level
measurements for each of the monitoring wells (P and PZ) were recorded and compared to
previous groundwater measurements recorded from 2009 through January 2023 by AMEC and
ENGEO. Groundwater elevation plots (hydrographs), including monthly precipitation totals, were
prepared for each monitoring well and are herein included in Appendix B.
Groundwater elevations between January 31, 2023 (date of last measurement by ENGEO) and
April 4, 2023 (date of initial measurement by Tetra Tech) correspond to the rainfall events that
produced 17.5 inches of rainfall. A review of the groundwater data during this period shows
increased groundwater elevations by up to 13.8 feet in 27 of the monitoring wells.
Continued monitoring of the horizontal drains was not included as part of this study due to low
output yields reported by ENGEO (2022).
5.2. INCLINOMETERS
Eight of the original 10 inclinometers (excluding to SI-1 and SI-7) were surveyed by Tetra Tech
in April 2023 to establish new baselines for comparison with future surveys. Establishment of
new baseline surveys were necessary since digital files provided by ENGEO for earlier 2019
surveys could not be readily merged with our inclinometer readings. At the time of this report, no
subsequent inclinometer readings have been collected, therefore, no conclusions regarding any
landslide movements can yet be developed. A supplemental report will be prepared at a later date
once additional data has been collected.
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6. HYDROGEOLOGIC AND ENGINEERING ANALYSES
6.1. GROUNDWATER FLOW AND GROUNDWATER MONITORING
North-facing descending topography with underlying bedrock units that dip to the north dominates
the Anaheim Hills area as indicated on the Geologic Map – Plate 1. Several prominent north to
northeast trending faults are also present and/or inferred beneath the study area. Under saturated
flow conditions, topography and geologic structure (bedding and faulting) can be dominant factors
that impact groundwater flow. For example, some of the high angle ancient faults identified by
E&S were interpreted as local groundwater barriers as well as possible conduits to transmit vertical
groundwater flow. In addition, portions of the higher elevations along the southerly ridgetop are
underlain by a plunging syncline structure or folded bedrock units that form a funnel-shaped
structural depression that directs subsurface flow toward the landslide.
Groundwater models were developed for this study utilizing the April 2023 monitoring well data
summarized within Section 5.1 of this report. By accurately plotting locations and elevations of
the groundwater surfaces measured from each monitoring well, contour lines representing surfaces
of equal elevation were created to depict the groundwater flow direction and gradient beneath the
SGHAD. The elevations utilized to create the groundwater models do not differentiate between
unconfined or confined aquifers, although fracture porosity is believed to provide connectivity
between aquifers.
By overlaying the April 2023 groundwater surface on the January 1993, February 1993,
October 1994 and August 1995 groundwater contour models prepared by E&S (1996), the current
groundwater conditions can be readily assessed to determine where current elevation fall beneath
or exceed the elevations of critical threshold levels identified within the E&S (1996) report and/or
established by the POC, and further discussed in Section 6.2 below. Graphic presentations
showing these relationships are presented in Appendix C. Cross-sectional profiles showing the
various groundwater levels through the body of the landslide mass are presented on Plate 4.
6.2. GROUNDWATER LEVELS
Analyses were performed as a part of this study to evaluate the effect of various groundwater levels
on the stability of the landslide. The landslide cross-sections, configuration, stratigraphy,
groundwater levels and material properties were taken directly from the seminal E&S (1996) report
that was the basis for the design and implementation of the current monitoring and dewatering
program. The report established several key groundwater conditions that need to be considered in
evaluation of the performance of the dewatering system and its effects on the landslide stability,
i.e., for assessment of the potential for landslide movement re-initiation. Specifically, the
following reference groundwater levels were established in the E&S (1996) report:
A. Groundwater at Landslide, i.e., groundwater at the time of landslide in January 1993 before
any groundwater control measures were implemented and landslide was still moving is
associated with a Factor of Safety of less than 1. This groundwater level is unacceptable as
it signifies a failure, ground movements, and ongoing damage.
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B. Groundwater at Movement Threshold, i.e., groundwater level in February 1993 when the
landslide movement halted. The associated Factor of Safety is expected to be slightly
above 1. This groundwater level is also unacceptable as it signifies an incipient failure.
C. Target Groundwater Level, i.e., groundwater level achieved in October 1994 when the
dewatering system was fully established and functional. This groundwater level is intended
to be maintained as it is deemed to provide an acceptable margin against re-initiation of
landslide movements. The slope stability Factors of Safety associated with this groundwater
level are greater than 1 and this groundwater level and the associated Factors of Safety are
referred to as “desirable”.
D. Limit Groundwater Level, i.e., groundwater level achieved in August 1995 when the
dewatering system was operating with some routine inefficiencies. This groundwater level
is considered the highest acceptable groundwater before the dewatering system needs to be
augmented to prevent re-initiation of landslide movements. The slope stability Factors of
Safety associated with this groundwater level are greater than 1 and this groundwater level
and the associated Factors of Safety are referred to as “acceptable”.
6.3. SLOPE STABILITY
The 1996 E&S analyses for the aforementioned groundwater levels were herein reproduced and
matched utilizing Slope/W slope stability software to form a basis for subsequent evaluation and
comparison of the actually observed, future, and any other investigated groundwater levels. The
summary of the slope stability analyses is provided in Table 4 below and the printout of the
analyses are included in Appendix D.
Table 4
Summary of Slope Stability Analyses
Groundwater: Landslide
(January 1993)
Movement
Threshold
(February 1993)
Target
“desirable”
(October 1994)
Limit
“acceptable”
(August 1995)
Current
(April 2023) Cross-Section
(slip surface)
Appendix page
1-1’
Appendix D-1a~1e 0.98 (0.96) 1.02 (1.01) 1.12 (1.09) 1.10 (1.08) 1.09
2-2’(upper)
Appendix D-2a~2e 1.02 (1.04) 1.09 (1.09) 1.22 (1.23) 1.16 (1.17) 1.20
3-3’(upper)
Appendix D-3a~3e 0.91 (0.99) 1.01 (1.09) 1.19 (1.28) 1.09 (1.19) 1.08
4-4’(upper)
Appendix D-4a~4e 0.98 (1.10) 1.09 (1.21) 1.25 (1.41) 1.20 (1.40) 1.14
Notes: Factors of Safety values in parenthesis are the values reported in the E&S (1996) report.
Factors of Safety in red indicate values below “desirable” Factor of Safety.
Factors of Safety in bold red indicate values below “acceptable” Factor of Safety.
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The key observations based on these analyses are provided below.
A. The analyses presented in the E&S (1996) report were satisfactorily reproduced and matched.
The numerical difference between the values presented in the E&S (1996) report and the
herein reproduced values are attributed to the use of different slope stability assessment
method as well as to the small differences in the geometry configuration due to digitization
of the geologic cross-sections from the E&S report.
B. The margin of safety expressed as the increment of the Factor of Safety over 1 for the Target
and Limit Groundwater levels is 0.12 to 0.25 and 0.09 to 0.20, respectively. Typically, a
margin of 0.5 or at least 0.3 is required for a slope to be considered acceptable or marginally
acceptable, respectively. This observation highlights that both the “desirable” and
“acceptable” Factors of Safety are lower than what would be conventionally considered
acceptable.
C. All Factors of Safety for the current groundwater condition (April 2023) are below the
“desirable” Factor of Safety values and all of the Factors of Safety, except for
Cross-Section 2-2’, are even below their respective “acceptable” Factor of Safety values.
This analysis is concerning as it indicates that the landslide in its current state is less stable
than what was established as minimally acceptable by the E&S (1996) report.
6.4. GROUNDWATER LEVEL EFFECT ON STABILITY
The groundwater levels within the landslide area are monitored by vertical observation wells at
37 locations. At 5 locations the groundwater is monitored by nested piezometers at 2 levels for a
total of 42 measurement points. It is notable that during the groundwater monitoring conducted
by Tetra Tech personnel for this study, the groundwater was above the Target Level in at least
20 locations and above the Limit Level in at least 10 locations. The groundwater elevations
measured during this study are at/near its highest level in at least 13 locations. This is a concerning
observation as higher groundwater signifies a lower stability.
It is, however, recognized that the individual groundwater measurement points do not sufficiently
describe the measure of stability. This is why we have developed a groundwater parameter to be
correlated with the slope stability, i.e., a Factor of Safety. This groundwater parameter
characterizes the overall quantity of the water affecting the slope stability and is determined
separately for each cross-section as the saturated area above the slip surface. This Groundwater
Index was calculated for all above-mentioned reference groundwater levels and calibrated against
additional groundwater levels in the range between the Limit Groundwater Level and the Target
Groundwater Level. This relationship of the Groundwater Index and the respective Factors of
Safety for each cross-section is presented in Chart 1 below.
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Chart 1 shows the current Factor of Safety for each cross-section as the large solid dot and the
Factor of Safety at the Limit Groundwater Level, i.e., “acceptable” Factor of Safety, as the large
open dot. The chart also allows a visual assessment of the margin of safety relative to the initiation
of the landslide that is signified for each cross-section by a colored dash. In short:
• the large open dot signifies acceptable condition; if the large solid dot is below the open dot,
the Factor of Safety is unacceptable;
• the distance between the large solid dot and the dash signifies the margin of safety before the
landslide could re-initiate.
The chart can also be used to estimate the Factor of Safety for any investigated groundwater level,
e.g., immediately after completion of the groundwater survey.
The key observation from this chart is that the current margin of safety relative to the expected
initiation of the landslide is less than 0.1 and, therefore; it does not take much increased
groundwater to approach a condition when re-initiation of the landslide is possible.
Chart 1. Factor of Safety as a function of GW Index. The large solid dot shows the current
(April 2023) stability; the open dots show the stability at Limit Groundwater Level. The
color dashes show where landslide movements are expected to be initiated.
Cross-Section 4-4'
y = -7E-06x + 1.2434
Cross-Section 2-2'
y = -9E-06x + 1.2285
Cross-Section 3-3'
y = -8E-06x + 1.1914
Cross-Section 1-1'
y = -2E-05x + 1.1223
0.90
0.95
1.00
1.05
1.10
1.15
1.20
1.25
1.30
1.35
0 10,000 20,000 30,000 40,000 50,000
Factor of SafetyGW Index
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6.5. POTENTIAL EFFECT OF DEWATERING SHUT-OFF
Currently, groundwater levels are managed through the existing dewatering system. It is of
particular interest to estimate how long it would take for the groundwater to rise sufficiently to
re-initiate the landslide movements if the existing dewatering system was shut off. Whereas
performance of a rigorous analysis would be extremely difficult and likely unreliable and
subjective because of the uncertainty and variability of virtually all input parameters, a simple
empirical assessment was instead performed as described below. The rationale of this assessment
is as follows:
1. It took about 20 months during 1993 and 1994 to lower the groundwater from the level at
Landslide to the Target Level.
2. The dewatering pumping system is reported (E&S, 1996) to had removed about 34.5 million
gallons (MG) of groundwater during this period.
3. Based on the geometry of the slip surface and the respective reference groundwater surfaces,
we can easily calculate the volume of the saturated landslide masses under each of the
reference groundwater surfaces (Column 1 in Table 5 below).
4. The volume of water available for release, i.e., movable water, from a soil mass can be
calculated by multiplying the soil mass volume by the effective porosity. Knowing that the
removal of 34.5 MG of groundwater by dewatering (Column 3 in Table 5) resulted in
lowering of the groundwater from the level at Landslide to the Target Level we also know
that the associated dewatered landslide mass volume is about 1.7 Mcy, i.e., 3 – 1.3 = 1.7 Mcy
(Column 1 in Table 5) and the effective porosity can be back-calculated. This effective
porosity is back-calculated as 0.1, which matches well with the values typical for fine-
grained materials.
5. Knowing that the current groundwater levels are similar to the Limit Groundwater Level we
can calculate that the water volume needed to achieve the Groundwater Level at Movement
Threshold is about 50 – 34 = 16 MG (Column 4 in Table 5).
6. Noting that the dewatering pumping system is typically removing about 1 MG of
groundwater per month, if the pumping is shut off, it will take about 16 months to reach the
February 1993 Groundwater Level at Movement Threshold, when the landslide movement
was halted and the landslide movement is therefore likely to re-initiate. By similar
calculation it would then take 26 months to reach the groundwater level at the time of the
landslide (Column 5 in Table 5).
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Table 5
Landslide Mass and Groundwater Quantities
Column #: 1 2 3 4 5
Groundwater Level
Volume of
Landslide Mass
below specified
groundwater level
Volume of
Movable Water
effective porosity neff = 0.1
Volumes of water to achieve specified
scenarios:
Mcy MG
At landslide
(1/20/1993) 3.0 60 60 – 26 = 34 MG
of groundwater
removed during
initial dewatering
to Target GW
level
60 – 34 = 26 MG
of infiltration
water to reach
the groundwater
level At
Landslide
At movement threshold
(2/15/1993) 2.5 50 50 – 34 = 16 MG
of infiltration
water to reach
the groundwater
level At
Movement
Threshold
Target
(10/5/1994) 1.3 26
Limit
(8/9/1995) 1.5 34
Notes: Mcy = 1,000,000 cy
MG = 1,000,000 gallons
City of Anaheim Project No. TET 22-236E
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7. CONCLUSIONS AND RECOMMENDATIONS
7.1. SGHAD FUNDING AND PROJECTED REVENUE RESOURCES
In 1999, the initial SGHAD capital was approximately $3,500,000. Recent financial projections
have estimated that the SGHAD funds will be exhausted by the end of the 2023 calendar year if
no additional sources of revenue are secured. Tetra Tech understands that at least 2 attempts were
recently made to approve a Board Resolution to establish an annual assessment to provide
continued funding for maintaining and monitoring of the dewatering system, both of which were
voted down by the SGHAD residents.
7.2. IMMINENT THREAT OF LANDSLIDE REACTIVATION
In the event that the SGHAD defaults on its obligation to maintain and effectively monitor the
dewatering system, the Santiago Landslide and possible surrounding properties will be in
imminent threat of landslide reactivation due to the resulting groundwater rise if no other
stabilizing measures are implemented.
7.3. SENSITIVITY OF GROUNDWATER CONTRIBUTIONS
From this study, we can conclude that recharge and discharge of groundwater within the limits of
the SGHAD are paramount factors that are key to the stability of the Santiago Landslide. For more
than 30 years, dewatering and monitoring efforts have proven to effectively manage the
groundwater regime during periods of intense rainfall and near constant irrigation and thus have
successfully mitigated re-activation of the Santiago Landslide.
This study has shown just how sensitive the Santiago Landslide is to groundwater fluctuations.
Under the current groundwater environment, the landslide is marginally stable. When
groundwater levels rise, the Factor of Safety against landslide re-activation decreases. Tetra
Tech’s estimates presented in Section 6.5, provide rough timeline for groundwater levels to rise to
past critical threshold limits and ultimately to levels that will induce re-activation of the landslide
if the dewatering system is shut off.
Rainfall and irrigation water have been identified as the primary contributors to surface water
infiltration within and around the SGHAD. Since options to mitigate infiltration due to rainfall
are limited, emphasis needs to be placed on irrigation controls in the event dewatering operations
are terminated until such time that a permanent solution can be implemented.
7.4. WATER CONSUMPTION ANALYSIS BY ANAHEIM PUBLIC UTILITIES
Concurrent with this study, the Anaheim Public Utilities (APU) conducted an analysis of water
usage in the SGHAD. The analysis utilized data from 305 residential water meters within the
SGHAD, and 10 residential water meters from a residential development (Point Premier) located
outside the limits of the SGHAD but within the elevated limits of the watershed contribution
boundaries shown on Exhibit 4. The purpose of this study was to determine a residential water
consumption baseline that allows for sufficient household water consumption with a portion of the
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allocation intended for modest outdoor irrigation uses. If implemented within the study area, the
residential water consumption baseline would provide the framework to significantly reduce
outdoor water use and hence, reduce groundwater recharge potential within the SGHAD.
A copy of APU’s water consumption analysis for the SGHAD is included within Appendix E. The
following presents a brief summary of their analysis. Data presented by APU is measured in
hundreds of cubic feet (HCF), where 1 HCF is equivalent to approximately 748 gallons of water.
Water meter data for the study area was collected in January 2023 to establish the average total
household water consumption (indoor and outdoor) during prolonged periods of precipitation and
cooler weather when many residents were likely not be using outdoor irrigation. Based on a review
of this data, the average household water consumption (indoor and outdoor) was approximately
11 HCF/meter/month.
Water meter data was also collected for the very dry January 2022 (7.84 annual rainfall total in
2022). Based on this review, an average household water consumption of 17 HCF/meter/month
was calculated for the month of January 2022. Over the entire 2022 calendar year, the average
water consumption was estimated to be 24 HCF/meter/month, with a summer peak in July 2022 at
29 HCF/meter/month.
Based on the presented analysis, APU recommended a residential water consumption of
15 HCF/meter/month which includes a modest water allocation for outdoor uses such as hand
watering of trees and drip irrigation. Since this monthly recommended water consumption value
is almost double the minimum health and safety needs for residents as established by the California
Department of Water Resources in their December 2021 State Water Project Allocation Notice for
California Water Contractors, the finding of the APU analysis was considered reasonable.
From this study, APU concluded that if a monthly water usage target of 15 HCF/month/meter is
established and enforced for the SGHAD property homeowners, a monthly water savings of up to
2 million gallons or 24 million gallons annually could be achieved. Assuming that these savings
are reflective of mostly irrigation recharge reduction and comparing these values to the
approximate annual yield from the existing dewatering system presented in Figure 5, it appears
that the reduced water consumption program could reduce groundwater recharge potential, and
thus reduce the demand for dewatering.
7.5. OUTDOOR WATER RESTRICTIONS
If it is determined that no other means are available to effectively dewater the SGHAD, as a
minimum, water restrictions to outdoor landscaping should be considered by the City of Anaheim.
While water restrictions are in no way intended to be an equivalent replacement to the current
dewatering system, future outdoor water restriction can provide extended time for alternative
planning prior to potential landslide re-activation. Obviously, the amount of time that could be
extended through water restrictions is dependent on the extent of successful implementation of
water restrictions.
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As a minimum, water restrictions should be implemented to restrict groundwater within the
SGHAD by a minimum of 1.5 times the annual dewatering discharge rates averaged over the last
7 years, or roughly 20 million gallons/year. This is intended to account for the highly complex
variables that can affect the recharge over such a large and geologically complex area.
Furthermore, outdoor irrigation should be completely suspended during rainfall events and should
not resume until such time that ground has sufficiently dried. Specific criteria for suspension and
continuation of outdoor watering during the rain months, along with tips for reducing outdoor
irrigation for landscaping can be found on the California Department of Water Resources website
at https://saveourwater.com/News- and- Events/Latest-News/Rainfall-is-Here.
The extent of the irrigation restrictions should include all properties within the watershed
contribution limits identified through this study and shown on Figure 4, which encompasses the
SGHAD and also includes approximately 60 additional acres of surrounding open space and
developed properties.
Regardless of the implementation of the irrigation restrictions and if any reduction in the
dewatering system is reduced or stopped, the groundwater monitoring within the SGHAD should
be continued and provided for geotechnical review on at least a monthly basis. Such groundwater
data could then be compared to the Groundwater Indices developed in Chart 1 in Section 6.5 of
this report, to assess the stability of the Santiago Landslide.
The findings of the independent APU study summarized herein provides a reasonable approach
for implementation of an outdoor water reduction program. If the outdoor water reduction program
is implemented and enforced to meet the anticipated outdoor water reduction goals, the time frame
for landslide re- activation can be prolonged to allow for implementation of alternative planning
and further mitigation measures. However, due to the inherent complexities to accurately estimate
how long it would take for the groundwater to rise sufficiently to re-activate the landslide, water
restriction options cannot be considered a solution for landslide mitigation and must be
accompanied by a comprehensive groundwater monitoring program until a permanent solution is
developed.
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8. LIMITATIONS
The conclusions, recommendations and opinions expressed in this report are based on Tetra Tech’s
review of background documents and on information obtained from this study. The findings of
this report may, therefore, need to be re-evaluate and revised as more data become available.
This document is intended to be used only in its entirety. No portion of the document, by itself, is
designed to completely represent any aspect of the project described herein. Tetra Tech should be
contacted if the reader requires additional information or has questions regarding the content,
interpretations presented, or completeness of this document. Reliance by others on the data
presented herein or for purposes other than those stated in the text is authorized only if so permitted
in writing by Tetra Tech. It should be understood that such an authorization may incur additional
expenses and charges.
Tetra Tech has endeavored to perform its evaluation using the degree of care and skill ordinarily
exercised under similar circumstances by reputable geotechnical professionals with experience in
this area in similar soil conditions. No other warranty, either expressed or implied, is made as to
the conclusions and recommendations contained in this report.
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9. SELECTED REFERENCES
AMEC Foster Wheeler, 2017, Annual Monitoring/Dewatering Summary, November 1, 2016
Through October 31, 2017, Santiago Landslide Area, Anaheim Hills, Anaheim, California,
Project No. IR13164620, December 18, 2017.
Benink & Slavens LLP, 2021, Demand for Arbitration, May 7, 202.
Bjorklund, T.; Burke, K.; Zhou, H. W.; and Yeats, R. S., 2002, Miocene rifting in the Los Angeles
basin: Evidence from the Puente Hills half-graben, volcanic rocks, and P-wave
tomography: Geology, Vol. 30, No. 5, pp. 451–454.
California Department of Water Resources, 2023, Save our Water,
https://saveourwater@water.ca.gov.
California Department of Water Resources, 2012, Reference Evapotranspiration Zones, California
Irrigation Management Information System, dated January 2012,
https://cimis.water.ca.gov
Cretelli, S.; Rumelhart, P. E.; And Ingersoll, R. V., 1995, Petrofacies and provenance of the Puente
Formation (middle to upper Miocene), Los Angeles Basin, southern California:
Implications for rapid uplift and accumulation rates: Journal Sedimentary Research, Vol.
A65, No. 4, pp. 656–667.
Eberhart and Stone, Inc., 1996, Santiago Landslide, Anaheim Hills, Anaheim, California:
unpublished consultant report, City of Anaheim, Office of City Attorney,
W.O. 165140.69, Volume I through VIIb, June 28, 1996, 69 p.
ENGEO, 2019a, 2019 1st Quarter Monitoring and Documentation, Santiago Geologic Hazard
Abatement District (GHAD), Anaheim Hills, Anaheim, California; Project Number
14174.000.000; March 28, 2019.
ENGEO, 2019b, 2019 2nd Quarter Monitoring and Documentation, Santiago Geologic Hazard
Abatement District (GHAD) Anaheim Hills, Anaheim, California; Project Number
14174.000.000; July 3, 2019.
ENGEO, 2019c, Limited Reconnaissance and Document Review, Slope Above Smokewood
Circle, Anaheim, California; Project Number 14174.000.000; June 6, 2019.
ENGEO, 2020a, Annual Monitoring Report – February 2019 through January 2020, Santiago
Geologic Abatement District (GHAD), Anaheim, California; Project Number
14174.002.019; April 21, 2020 (Revised June 5, 2020).
ENGEO, 2020b, 2020 Monitoring Event and Documentation No. 1, Santiago Geologic Hazard
Abatement District (GHAD), Anaheim, California; Project Number 14174.002.019; April
21, 2020.
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ENGEO, 2020c, 2020 Monitoring Event and Documentation 2nd Quarter, Santiago Geologic
Hazard Abatement District (GHAD), Anaheim, California; Project Number
14174.002.019; July 27, 2020.
ENGEO, 2020d, Horizontal Drains Monitoring and Documentation, Santiago Geologic Hazard
Abatement District (GHAD), Anaheim, California; Project Number 14174.002.019; July
27, 2020.
ENGEO, 2020e, 2020 Annual Monitoring Report, Santiago Geologic Hazard Abatement District
(GHAD), Anaheim, California. Project Number 14174.002.020. November 6, 2020.
ENGEO, 2020f, 1ˢᵗ Semi-Annual Vertical Well Observation Report Fiscal Year 2020/21
Monitoring Event and Documentation, Santiago Geologic Hazard Abatement District
(GHAD), Anaheim, California; Project Number 14174.002.020; October 27, 2020.
ENGEO, 2020g, October 2020 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; October 27, 2020.
ENGEO, 2021a, November 2020 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; January 14, 2021.
ENGEO, 2021b, December 2020 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; January 14, 2021.
ENGEO, 2021c, January 2021 – Monthly Comparison of Groundwater Discharge Volumes and
Post –Rain Event Horizontal Drains, Vertical Piezometers, and Monitoring Well
Observation Report, Santiago Geologic Hazard Abatement District (GHAD), Anaheim,
California; Project Number 14174.002.020; April 14, 2021.
ENGEO, 2021d, February 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; April 14, 2021.
ENGEO, 2021e, March 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; April 14, 2021.
ENGEO, 2021f, April 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; May 28, 2021.
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ENGEO, 2021g, May 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; June 1, 2021.
ENGEO, 2021h, June 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.020; July 6, 2021.
ENGEO, 2021i, July 2021 – Monthly Comparison of Groundwater Discharge Volumes, Santiago
Geologic Hazard Abatement District (GHAD), Anaheim, California; Project Number
14174.002.021; September 3, 2021.
ENGEO, 2021j, August 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.021; September 15, 2021.
ENGEO, 2021k, September 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number 14174.002.021; September 28, 2021.
ENGEO, 2021l, October 2021 – Monthly Comparison of Groundwater Discharge Volumes,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California; Project
Number14174.002.021; October 27, 2021.
ENGEO, 2021m, Annual Monitoring Report, Santiago Geologic Hazard Abatement District
(GHAD), Anaheim, California. Project Number 14174.002.021. October 29, 2021.
ENGEO, 2021n, Pre-Rain Season Piezometers and Monitoring Wells Observations Report,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.021. November 18, 2021.
ENGEO, 2021o, Monthly Comparison of Groundwater Discharge Volumes – November 2021,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.021. December 17, 2021.
ENGEO, 2022a, Post-Rain Event Piezometers and Monitoring Wells Observations Report,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.021. February 9, 2022.
ENGEO, 2022b, Monthly Comparison of Groundwater Discharge Volumes – December 2021,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.021. February 10, 2022.
ENGEO, 2022c, Monthly Comparison of Groundwater Discharge Volumes – February 2022,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.021. March 8, 2022.
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ENGEO, 2022d, Monthly Comparison of Groundwater Discharge Volumes – March 2022,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.021. April 18, 2022.
ENGEO, 2022e, Monthly Comparison of Groundwater Discharge Volumes – April 2022,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.021. April 28, 2022.
ENGEO, 2022f, May 2022 Monthly Comparison of Groundwater Discharge Volumes and
Horizontal Drain Observation Report, Santiago Geologic Hazard Abatement District
(GHAD), Anaheim, California. Project Number 14174.002.021. June 21, 2022.
ENGEO, 2022g, Monthly Comparison of Groundwater Discharge Volumes – June 2022, Santiago
Geologic Hazard Abatement District (GHAD), Anaheim, California. Project Number
14174.002.021. July 8, 2022.
ENGEO, 2022h, Monthly Comparison of Groundwater Discharge Volumes – July 2022, Santiago
Geologic Hazard Abatement District (GHAD), Anaheim, California. Project Number
14174.002.022. September 1, 2022.
ENGEO, 2022i, Monthly Comparison of Groundwater Discharge Volumes – August 2022,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.022. September 8, 2021.
ENGEO, 2022j, Monthly Comparison of Groundwater Discharge Volumes – September 2022,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.022. October 25, 2022.
ENGEO, 2022k, Monthly Comparison of Groundwater Discharge Volumes – October 2022,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.022. October 25, 2022.
ENGEO, 2022l, Annual Monitoring Report, Santiago Geologic Hazard Abatement District
(GHAD), Anaheim, California. Project Number 14174.002.022. October 27, 2022.
ENGEO, 2023a, Monthly Comparison of Groundwater Discharge Volumes and Post-Rain Events
Vertical Piezometers and Monitoring Well Observation Report – January 2023, Santiago
Geologic Hazard Abatement District (GHAD), Anaheim, California. Project Number
14174.002.022. February 13, 2023.
ENGEO, 2023b, Monthly Comparison of Groundwater Discharge Volumes – February 2023,
Santiago Geologic Hazard Abatement District (GHAD), Anaheim, California. Project
Number 14174.002.022. March 15, 2023.
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ENGEO, 2023c, Monthly Comparison of Groundwater Discharge Volumes – May 2023, Santiago
Geologic Hazard Abatement District (GHAD), Anaheim, California. Project Number
14174.002.022. May 24, 2023.
Gath, E. M. and Grant, L. B., 2002, Is the Elsinore Fault responsible for the uplift of the Santa Ana
Mountains, Orange County, California: Geological Society America, Abstracts with
Programs, Vol. 34, No. 5, pp. A–87.
Hevesi, J.A., and Johnson, T.D., 2016, Estimating spatially and temporally varying recharge and
runoff from precipitation and urban irrigation in the Los Angeles Basin, California: U.S.
Geological Survey Scientific Investigations Report 2016–5068,
192 p., http://dx.doi.org/10.3133/sir20165068.
Johnson, Philip, L., and Cotton, Willian, R., 2005, The Santiago Landslide and Associated Ridge-
top Graben (Sackungen): Implications for Paleoseismic Landslide Studies, Environmental
& Engineering Geosciences, Vol. XI, No. 1, February 2005, pp. 5 – 15.
McLarty, Mark, W., and Clark, Donald, W., 1998, Geomorphology & Geology Defining the
Santiago Landslide 1992 – 1993, dated October 6, 1998.
McLarty, Mark, W., and Clark, Donald, W., 1999, Plan of Control Prepared for Proposed Santiago Geologic Hazard Abatement District, Anaheim Hills, Anaheim, California, dated February 22, 1999.
Morton, P. K., and Miller, R.V., 1973, Geologic Map of Orange County, California, California
Department of Conservation, Division of Mines and Geology, CDMG Preliminary
Report 15.
Schoellhamer, J. E.; Yerkes, R. F.; Kinney, D. M.; And Vedder, J.G., 1954, Geologic Map of the
Northern Santa Ana Mountains, Orange and Riverside Counties: U.S. Geological Survey
Professional Oil and Gas Investigations Map OM-154.
Schoellhamer, J. E.; Vedder, J. G.; Yerkes, R. F.; And Kinney, D.M., 1981, Geology of the
Northern Santa Ana Mountains: U.S. Geological Survey Professional Paper 420D, 107 p.
Tan, Siang S., 1992, Landslide Hazards in the North Half of the Black Star Canyon Quadrangle,
Orange and Riverside Counties, California, California Department of Conservation,
Division of Mines and Geology, CDMG Open-File Report 90-10.
Wood, 2018, Annual Monitoring/Dewatering Summary, November 1, 2017 Through October 31,
2018, Santiago Landslide Area, Anaheim Hills, Anaheim, California, Project No.
IR13164620, December 24, 2018.
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PLATES
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765PROJECT NO.:DATE:DRAWN BY:TETRA TECHTEL 909.860.777 www.tetratech.comGRAPHIC SCALE:1''=TET 22-236E JUNE 2023DLPLATE 1SANTIAGO LANDSLIDESGHAD FACILITIES LOCATION PLAN500100 200100'NOTE: Base map produced by AMEC, Dec 2012
20
22 Tps
Tps
Tps
Tps
f
18
27
15
10
15
20
24
12
8
40
18
38
10
22
18
33
11
33
19
Tps
Tps
Qls
Tps
69
14
30
30
10
53
86
54
54
50
25
Tt?19
11
22
24
25
22
23
6
27
25
5
10
9
16
6
10
16
18
20
28
14
Temb
Tps
Qal
Qls
Tt
Tplv
Tps
af
16
16
19
12
10
33
19
27
Tt
Tt
Tt
Tt
35
25
14
18
18
41
14
10
32
17
23
19
19
20
26
Qal
Tplvss
40
Tplvss
af
Tps
af
af
Tps
af
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af
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af
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18
af
22
16
17
17
69
80-85
Tplvslt
Tplvslt
Tplvslt
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Tplvslt
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Tplvslt
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Tplvss ????
?????Tt
Tt
TtTt
Tt
Tplvss
Tplvslt
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Tplvslt
??
Tplvslt
af
af
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Tplvslt
Tplvslt
Tps
27
?
20
40
?Tplvslt
Tt
afaf
Temb Temb Temb
?11
af
Tps
27??af
Tplvslt
Tps
47
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65
42
32
20
70
30-40
54-74
40
60
29
@934.7'
@933.5'
@933.5'
@931.2'
@931.1'
@929.5'
@928.5'
@928'
@926.9'
@925.5'
@925.5'
@921.5'
TD = 25' (916.5' elev)
26-35 @932'
@928.5'
23 @925.3'
44 @925'
19 @922.0'
25 @920.5'
48
TD = 25' (869' elev)
80
5
5
5
5
36
54
33
20
20
17
20
@938'
@935'
@932'
@929.6'
@927'
@920.5'
@911.8'
@910'
@907.5'
@906.5'
@905.5'
TD = 50' (892' elev)
5 @917.5'23 @903.2'
@904.7'
25 @900'
Tplvslt
20
18
24
21
@922'
@908'
TD = 75' (869' elev)
2
2'
3
Tplvslt
1
1'
4'
4
3'????
?
Qal
RESISTANT SANDSTONE BED Temb ?TplvssGEORGETOWNT-1
T-2
14
T-3
45
42
@1038'
@1033.2'
@1031.7'
@1029.2'
@1027'
@1023.4'
@1023'
@1021.3'
@997'
@992.8'
@991'
@988'
@986.8'
@984.5'
@980'
@980'
@976'
34
45
25
32
45
45
60
66
45
68
30
28
27
27
25
TD = 82' (972' elev)
35
@1009'
22 @997'
27 @991'
21 @984'
47 @993'
TD = 100' (918' elev)
B-1
B-5
B-6
18
B-4
B-3
B-2
SI-7
SI-2
T-4
SI-6
SI-5
T-5
SI-9
SI-10
SI-1 A.D.S FAULTA.D.S FAULTB-7
(Incipient Toe)RIMWOODFAULTZONEaf
SI-3
SI-4
SI-8
DW-11
DW-18
DW-8
DW-15
DW-9
DW-14
DW-7
DW-20
DW-5
DW-29
DW-6
DW-4
DW-17
DW-3DW-10
DW-1
DW-13
DW-22
DW-35
DW-19
DW-2
DW-27
DW-34
DW-33
DW-16
DW-12
DW-31
DW-21
DW-30
DW-32
DW-28
DW-26
P-10
P-18
P-16
P-28
P-20
P-15
P-6
P-5
P-1
P-21
P-19
P-26
P-25
P-27
P-17
P-9
PZ-5
P-13
P-11
P-23
P-14
P-8 P-12
PZ-2
P-3
P-7
P-22
P-24
PZ-3
P-4
PZ-1
PZ-4
P-2
DW-38
DW-36
DW-39
DW-41
B-8
DW-37
DEVELOPMENT OF TOE UNCERTAIN
RELATIVELY MINOR DISPLACEMENT OBSERVED
Pressure RidgeLandslide ToePressureRidgeLandslide HeadscarpTension CracksTension CracksHeadscarpHeadscarpM.W.D SANTIAGO LATERAL
TRENCH TUNNEL
DEVELOPMENT OF
LATERAL MARGIN UNCERTAIN
NO GROUND DISPLACEMENT OBSERVED
DEVELOPMENT OF
LATERAL MARGIN UNCERTAIN
NO GROUND DISPLACEMENT
OBSERVED FAULTP-26BP-26C
P-22BP-22C
P-25B
P-25C
PT-APT-B
P-A
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765 PROJECT NO.:DATE:DRAWN BY:
TETRA TECH
TEL 909.860.777 www.tetratech.com
GRAPHIC SCALE:1''=
TET 22-236E JUNE 2023 DL PLATE 2
SANTIAGO LANDSLIDE
GEOLOGIC MAP500100 200
100'
LEGEND
(LOCATIONS APPROXIMATE)
P-28
DW-42
T-4
Tps
af
24
60
B-1
SI-5
PZ-5
Tplv
Temb
Qls
Qal
Tt
Artificial Fill
Alluvium
Landslide Debris
Puente Formation - Soquel Member
Puente Formation - La Vida Member
(slt - siltstone, ss - sandstone)
El Modeno Volcanics - Basalt
Topanga Formation
Observation Well
Piezometer/Core Boring
Dewatering Well
Exploratory Boring
Utility Excavation Trench
Inclinometer
Bedding Attitude
(dashed where buried or encountered
within the M.W.D.)
Fault or Shear Attitude
?
Geologic Contact
(queried where uncertain)
?
Fault
(soild where well located, dashed where approx. located, querried
where uncertain, dotted where concealed by fill)
65
Anticline
(Solid where well located, dashed where approx.
located, queried where continuation or existence
uncertain, arrow indicates direction of plunge)
?
?Syncline
(Solid where well located, dashed where approx.
located, queried where continuation or existence
uncertain, arrow indicates direction of plunge)
Santiago Landslide (E&S)
(Boundry as defined by mapped ground
deformations, landslide features labeled where
defined)
4'4 Geologic Cross-Section
NOTE: Geologic information modified from Eberhart & Stone, 1996
4 4'
900
800
700
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400P-11 (proj. 48')P-2 (proj. 63')P-19 (proj. 89')P-10 (proj. 90')P-6 (proj. 110')P-4P-23 (proj. 23')P-21 (proj. 95')P-15P-6 (proj. 66')P-1 (proj. 20')900
800
700
1000
1100
1000
110033'
940
840
740
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400
940
840
740
1040
1140
1040
1140
1 1'
960
860
760
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400
960
860
760
1060
1160
1060
1160 2 2'
940
840
740
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400
940
840
740
1040
1140
1040
1140
P-5 (proj. 215')P-1 (proj. 170')P-20 (proj. 20')Vassar Cir.
Serrano Ave.Georgetown Cir.Ave. De Santiago
Serrano Ave.
Serrano Ave.Leafwood Dr.
Rimwood Dr.
Ave De
Santiago
Ave De
Santiago
Georgetown
Cir.
Ave De
Santiago
Ave De
Santiago
TET 22-236E DL PLATE 3
SANTIAGO LANDSLIDE
GEOLOGIC CROSS SECTIONS 1-1' THROUGH 4-4'500 100 200
100'
JUNE 2023
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765 PROJECT NO.:DATE:DRAWN BY:
TETRA TECH
TEL 909.860.777 www.tetratech.com
GRAPHIC SCALE:1''=NOTE: Cross-Sections modified from Eberhart & Stone, 1996
4 4'
900
800
700
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400P-11 (proj. 48')P-2 (proj. 63')P-19 (proj. 89')P-10 (proj. 90')P-6 (proj. 110')P-4P-23 (proj. 23')P-21 (proj. 95')P-15P-6 (proj. 66')P-1 (proj. 20')900
800
700
1000
1100
1000
110033'
940
840
740
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400
940
840
740
1040
1140
1040
1140
1 1'
960
860
760
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400
960
860
760
1060
1160
1060
1160 2 2'
940
840
740
1000 200 300 400 500 600 700 800 900 1000 1100 1200 1300 1400
940
840
740
1040
1140
1040
1140
P-5 (proj. 215')P-1 (proj. 170')P-20 (proj. 20')Vassar Cir.
Serrano Ave.Georgetown Cir.
Serrano Ave.
Serrano Ave.Leafwood Dr.
Rimwood Dr.
Ave De
Santiago
Ave De
Santiago
Georgetown
Cir.
Ave De
Santiago
Ave De
Santiago
Ave De
Santiago
TET 22-236E DL Plate 4
SANTIAGO LANDSLIDE
GROUNDWATER PROFILES THROUGH
LANDSLIDE MASS
500 100 200
100'
JUNE 2023
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765 PROJECT NO.:DATE:DRAWN BY:
TETRA TECH
TEL 909.860.777 www.tetratech.com
GRAPHIC SCALE:1''=
Landslide failure surface
Current groundwater - April 2023
Groundwater at landslide failure - January 1993
Target groundwater - October 1994
Limit groundwater - August 1995
LEGEND
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
36
APPENDIX A
Cumulative and Incremental Plots of Inclinometer Surveys for SI-4
(Wood, 2018)
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
37
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
38
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
39
Appendix B
Groundwater Elevation Plots (Hydrographs) with Monthly Precipitation
0123456789109409509609709809901,0001,0101,0201,0301,040Rainfall (in)Elevation (ft)P-1Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-1
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)P-2Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-2
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)P-3Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-3
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)P-4Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-4
012345678910830840850860870880890900910920930Rainfall (in)Elevation (ft)P-5Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-5
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)P-6Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-6
012345678910810820830840850860870880890900910Rainfall (in)Elevation (ft)P-7Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-7
012345678910790800810820830840850860870880890Rainfall (in)Elevation (ft)P-8Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-8
012345678910780790800810820830840850860870880Rainfall (in)Elevation (ft)P-9Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-9
012345678910790800810820830840850860870880890Rainfall (in)Elevation (ft)P-10Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-10
012345678910780790800810820830840850860870880Rainfall (in)Elevation (ft)P-11Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-11
012345678910770780790800810820830840850860870Rainfall (in)Elevation (ft)P-12Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-12
012345678910780790800810820830840850860870880Rainfall (in)Elevation (ft)P-13Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-13
012345678910790800810820830840850860870880890Rainfall (in)Elevation (ft)P-14Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-14
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)P-15Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-15
012345678910740750760770780790800810820830840Rainfall (in)Elevation (ft)P-16Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-16
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)P-17Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-17
012345678910700710720730740750760770780790800Rainfall (in)Elevation (ft)P-18Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-18
012345678910900910920930940950960970980Rainfall (in)Elevation (ft)P-19Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-19
0123456789109409509609709809901,0001,0101,0201,0301,040Rainfall (in)Elevation (ft)P-20Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-20
0123456789109209309409509609709809901,0001,0101,020Rainfall (in)Elevation (ft)P-21Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-21
0123456789109009109209309409509609709809901,000Rainfall (in)Elevation (ft)P-22Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-22
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)P-22BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-22B
012345678910880890900910920930940950960970980Rainfall (in)Elevation (ft)P-22CRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-22C
012345678910850860870880890900910920930940950Rainfall (in)Elevation (ft)P-23Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-23
012345678910850860870880890900910920930940950Rainfall (in)Elevation (ft)P-24Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-24
0123456789109209309409509609709809901,0001,0101,020Rainfall (in)Elevation (ft)P-25Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-25
012345678910830840850860870880890900910920930940950Rainfall (in)Elevation (ft)P-25BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-25B
0123456789109109209309409509609709809901,0001,0101,020Rainfall (in)Elevation (ft)P-25CRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-25C
0123456789109109209309409509609709809901,0001,010Rainfall (in)Elevation (ft)P-26Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-26
012345678910830840850860870880890900910920930940950Rainfall (in)Elevation (ft)P-26BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-26B
0123456789109009109209309409509609709809901,000Rainfall (in)Elevation (ft)P-26CRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-26C
012345678910850860870880890900910920930940950Rainfall (in)Elevation (ft)P-27Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-27
012345678910800810820830840850860870Rainfall (in)Elevation (ft)P-28Rainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-28
0123456789109809901,0001,0101,0201,0301,0401,0501,0601,0701,080Rainfall (in)Elevation (ft)P-ARainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWP-A
0123456789109809901,0001,0101,0201,0301,0401,0501,0601,0701,080Rainfall (in)Elevation (ft)PT-ARainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPT-A
0123456789109009109209309409509609709809901,000Rainfall (in)Elevation (ft)PT-BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPT-B
012345678910760770780790800810820830840850860Rainfall (in)Elevation (ft)PZ-1CRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-1C
012345678910720730740750760770780790800810820Rainfall (in)Elevation (ft)PZ-1DRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-1D
012345678910810820830840850860870880890900910Rainfall (in)Elevation (ft)PZ-2ARainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-2A
012345678910710720730740750760770780790800810820830840850Rainfall (in)Elevation (ft)PZ-2CRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-2C
012345678910840850860870880890900910920930940Rainfall (in)Elevation (ft)PZ-3BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-3B
012345678910770780790800810820830840850860870880890Rainfall (in)Elevation (ft)PZ-3CRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-3C
012345678910850860870880890900910920930940950Rainfall (in)Elevation (ft)PZ-4BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-4B
012345678910800810820830840850860870880890900Rainfall (in)Elevation (ft)PZ-4CRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-4C
012345678910750760770780790800810820830840850Rainfall (in)Elevation (ft)PZ-5BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-5B
012345678910660670680690700710720730740750760770780790800810820830840850Rainfall (in)Elevation (ft)PZ-5BRainfall DataStandpipe BottomGW @LandslideTarget GWLimiting GWPZ-5C
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
40
Appendix C
Graphic Relationships of Various Groundwater Surfaces
(Plates C-1 through C-4)
© 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS © 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS
800800
850900950810820830840860870
880890910920930940960970
950920930940960970
980850 900820830840860870880890910
920920
2
2'
3
1
1'
4'
4
3'990
1000
970
980
990
1010
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765 PROJECT NO.:DATE:DRAWN BY:
TETRA TECH
TEL 909.860.777 www.tetratech.com
SANTIAGO LANDSLIDE
N:\02 - PROJECTS\2022\TET 22-236E (4552-0236) Santiago Landslide GHAD - Anaheim Hills\06 Drafting\GW - Slip Surface Contours\Groundwater Contours.dwg 6/13/2023 3:52 PMLEGEND
CURRENT GROUNDWATER SURFACE CONTOUR
CURRENT GW BELOW GW AT LANDSLIDE
JANUARY 20, 1993 GROUNDWATER SURFACE CONTOUR
0
GRAPHIC SCALE:1''=
50
100'
100 200FEBRUARY 2023 GROUNDWATER ELEVATIONS AND GROUNDWATER ELEVATIONS AT LANDSLIDE (1/20/1993)
APPROXIMATE LIMITS OF LANDSLIDE, MODIFIED BY TETRA TECH
RELATIONSHIP OF
CURRENT GW AND GW AT LANDSLIDE
TET 22-236E CLM PLATE C1JUNE 2023
© 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS © 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS 800850900950780790810820830840860
870
880
890910920930940960950920930940960970
980850 900820830840860870880890910
920920
2
2'
3
1
1'
4'
4
3'990
1000
960
970
980
990
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765 PROJECT NO.:DATE:DRAWN BY:
TETRA TECH
TEL 909.860.777 www.tetratech.com
SANTIAGO LANDSLIDE
N:\02 - PROJECTS\2022\TET 22-236E (4552-0236) Santiago Landslide GHAD - Anaheim Hills\06 Drafting\GW - Slip Surface Contours\Groundwater Contours.dwg 6/13/2023 3:50 PMLEGEND
CURRENT GROUNDWATER SURFACE CONTOUR
FEBRUARY 15, 1993 GROUNDWATER SURFACE CONTOUR
0
GRAPHIC SCALE:1''=
50
100'
100 200
FEBRUARY 2023 GROUNDWATER ELEVATIONS AND
GROUNDWATER ELEVATIONS AT MOVEMENT THRESHOLD (2/15/1993)
APPROXIMATE LIMITS OF LANDSLIDE, MODIFIED BY TETRA TECH
RELATIONSHIP OF CURRENT GW
AND GW AT MOVEMENT THRESHOLD
TET 22-236E CLM PLATE C2JUNE 2023
CURRENT GW BELOW GW AT MOVEMENT THRESHOLD
CURRENT GW 0' TO 15' ABOVE GW AT MOVEMENT THRESHOLD
GW AT MOVEMENT THRESHOLD NOT ESTABLISHED
© 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS © 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS
850
810
820
830
840
860
8708708809
0
0
950 88089091
0
92
0
93
0
940
960
970950920930940960970
980850 900820830840860870880890910
920920
2
2'
3
1
1'
4'
4
3'990
LEGEND
CURRENT GROUNDWATER SURFACE CONTOUR
CURRENT GW BELOW TARGET GW
OCTOBER 5, 1994 GROUNDWATER SURFACE CONTOUR
CURRENT GW 0' TO 20' ABOVE TARGET GW
40' TO 60' ABOVE TARGET GW
60' TO 80' ABOVE TARGET GW
80' TO 100' ABOVE TARGET GW
100' TO 120' ABOVE TARGET GW
0
GRAPHIC SCALE:1''=
50
100'
100 200
20' TO 40' ABOVE TARGET GW
TARGET GROUNDWATER NOT ESTABLISHED
FEBRUARY 2023 GROUNDWATER ELEVATIONS AND TARGET GROUNDWATER ELEVATION (10/5/1994)
APPROXIMATE LIMITS OF LANDSLIDE, MODIFIED BY TETRA TECH
RELATIONSHIP OF
CURRENT GW AND TARGET GW
TET 22-236E CLM PLATE C3JUNE 2023
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765 PROJECT NO.:DATE:DRAWN BY:
TETRA TECH
TEL 909.860.777 www.tetratech.com
SANTIAGO LANDSLIDE
N:\02 - PROJECTS\2022\TET 22-236E (4552-0236) Santiago Landslide GHAD - Anaheim Hills\06 Drafting\GW - Slip Surface Contours\Groundwater Contours.dwg 6/13/2023 3:49 PM
© 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS © 2023 Microsoft Corporation © 2023 Maxar ©CNES (2023) Distribution Airbus DS
850
90
0
950
810 820830
840
860
870
88
0
8
9
0
910
920
930
940
960
97
0950920930940960970
980850 900820830840860870880890910
920920
2
2'
3
1
1'
4'
4
3'990
21700 Copley Drive, Suite 200, Diamond Bar, CA 91765 PROJECT NO.:DATE:DRAWN BY:
TETRA TECH
TEL 909.860.777 www.tetratech.com
SANTIAGO LANDSLIDE
N:\02 - PROJECTS\2022\TET 22-236E (4552-0236) Santiago Landslide GHAD - Anaheim Hills\06 Drafting\GW - Slip Surface Contours\Groundwater Contours.dwg 6/13/2023 3:49 PMLEGEND
CURRENT GROUNDWATER SURFACE CONTOUR
CURRENT GW BELOW LIMIT GW
AUGUST 9, 1995 GROUNDWATER SURFACE CONTOUR
CURRENT GW 0' TO 20' ABOVE LIMIT GW
40' TO 60' ABOVE LIMIT GW
60' TO 80' ABOVE LIMIT GW
80' TO 100' ABOVE LIMIT GW
100' TO 120' ABOVE LIMIT GW
0
GRAPHIC SCALE:1''=
50
100'
100 200
20' TO 40' ABOVE LIMIT GW
LIMIT GROUNDWATER NOT ESTABLISHED
FEBRUARY 2023 GROUNDWATER ELEVATIONS AND LIMIT GROUNDWATER ELEVATIONS (8/9/1995)
APPROXIMATE LIMITS OF LANDSLIDE, MODIFIED BY TETRA TECH
RELATIONSHIP OF
CURRENT GW AND LIMIT GW
TET 22-236E CLM PLATE C4JUNE 2023
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
41
Appendix D
Slope Stability
0.98Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Description: Static Stability at Time of Failure, Jan 1993Analysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 1-1'Color NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33Rimwood FaultFault ZoneAve. De SantiagoRimwood Dr.D-1a
1.02Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Description: Static Stability Post Failure, Feb 1993Analysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 1-1'Color NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33Rimwood FaultFault ZoneAve. De SantiagoRimwood Dr.D-1b
1.10Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Description: Static Stability GW Limit Level, 1995Analysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 1-1'Color NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33Rimwood FaultFault ZoneAve. De SantiagoRimwood Dr.D-1c
1.12Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Description: Static Stability Target GW, 1994Analysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 1-1'Color NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33Rimwood FaultFault ZoneAve. De SantiagoRimwood Dr.D-1d
1.09Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Elevation (ft)7608008408809209601,0001,0401,0801,1201,1601,200Description: Static Stability Current GWAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 1-1'Color NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33Rimwood FaultFault ZoneAve. De SantiagoRimwood Dr.Ave. De SantiagoRimwood Dr.D-1e
1.02Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability at Time of Failure, Jan 1993, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 2-2'Rimwood FaultFault ZoneFault ZoneSerrano Ave.Leafwood Dr.Ave. De SantiagoTiebackColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-2a
1.09Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability Post Failure, Feb 1993, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 2-2'Rimwood FaultFault ZoneFault ZoneSerrano Ave.Leafwood Dr.Ave. De SantiagoTiebackColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-2b
1.16Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability GW Limit Level, 1995, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 2-2'Rimwood FaultFault ZoneFault ZoneSerrano Ave.Leafwood Dr.Ave. De SantiagoTiebackColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-2c
1.22Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability Target GW, 1994, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 2-2'Rimwood FaultFault ZoneFault ZoneSerrano Ave.Leafwood Dr.Ave. De SantiagoTiebackColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-2d
1.20Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability Current GW, Upper Failure SurfaceAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 2-2'Rimwood FaultFault ZoneFault ZoneSerrano Ave.Leafwood Dr.Ave. De SantiagoTiebackColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-2e
0.91Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability with GW at Failure, Jan 1993, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 3-3'Fault ZoneFault ZoneRimwood FaultSerrano Ave.Georgetown Cir.Ave. De Santiago Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface 127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-3a
1.01Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability with GW Post Failure, Feb 1993, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 3-3'Fault ZoneFault ZoneRimwood FaultSerrano Ave.Georgetown Cir.Ave. De Santiago Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface 127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-3b
1.09Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability GW Limit Level, 1995, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 3-3'Fault ZoneFault ZoneRimwood FaultSerrano Ave.Georgetown Cir.Ave. De Santiago Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface 127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-3c
1.19Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability Target GW, 1994, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 3-3'Fault ZoneFault ZoneRimwood FaultSerrano Ave.Georgetown Cir.Ave. De Santiago Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface 127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-3d
1.08Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7407808208609009409801,0201,0601,100Elevation (ft)7407808208609009409801,0201,0601,100Description: Static Stability Current GW, Upper Failure SurfaceAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 3-3'Fault ZoneFault ZoneRimwood FaultSerrano Ave.Georgetown Cir.Ave. De Santiago Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface 127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-3e
0.98Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7007407808208609009409801,0201,060Elevation (ft)7007407808208609009409801,0201,060Description: Static Stability with GW at Failure, Jan 1993, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 4-4'A.D.S. Fault ZoneFault ZoneRimwood FaultSerrano Ave.Vassar Cir.Georgetown Cir.Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-4a
1.09Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7007407808208609009409801,0201,060Elevation (ft)7007407808208609009409801,0201,060Description: Static Stability with GW post Failure, Feb 1993, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 4-4'A.D.S. Fault ZoneFault ZoneRimwood FaultSerrano Ave.Vassar Cir.Georgetown Cir.Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-4b
1.20Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7007407808208609009409801,0201,060Elevation (ft)7007407808208609009409801,0201,060Description: Static Stability with GW Limit Level, 1995, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 4-4'A.D.S. Fault ZoneFault ZoneRimwood FaultSerrano Ave.Vassar Cir.Georgetown Cir.Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-4c
1.25Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7007407808208609009409801,0201,060Elevation (ft)7007407808208609009409801,0201,060Description: Static Stability Target GW, 1994, Upper FailureAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 4-4'A.D.S. Fault ZoneFault ZoneRimwood FaultSerrano Ave.Vassar Cir.Georgetown Cir.Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-4d
1.14Distance (ft)0100200300400500600700800900 1,000 1,100 1,200 1,300 1,400Elevation (ft)7007407808208609009409801,0201,060Elevation (ft)7007407808208609009409801,0201,060Description: Static Stability Current GW, Upper Failure SurfaceAnalysis Type: Morgenstern-PriceOptimize Critical Slip Surface Location: YesDate: 06/02/2023Anaheim HillsSantiago LandslideSection 4-4'A.D.S. Fault ZoneFault ZoneRimwood FaultSerrano Ave.Vassar Cir.Georgetown Cir.Ave. De SantiagoColor NameUnit Weight (pcf)Effective Cohesion (psf)Effective Friction Angle (°)Af - Artificial Fill120 150 20Failure Surface127 100 11Tplv - La Vida Member, Puente Formation124 100 15Tps - Soquel Member, Puente Formation127 100 33D-4e
City of Anaheim Project No. TET 22-236E
Geotechnical Evaluation & Groundwater Impact Assessment July 5, 2023
42
APPENDIX E
Water Consumption Analysis for the Santiago Geological Hazard Abatement District
(Anaheim Public Utilities Department, dated June 19, 2023)