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CHAPTER 5
In-Situ Evaluation of Initial State of Lumpy Fill
5.1 Introduction
When clay lumps are used for reclamation, the fill form will have large inter-
lump voids initially. If these large voids do not close completely, even with surcharge,
this will lead to serious long-term settlement when a structure is constructed on it.
Therefore, it is important to understand the behavior of such a fill at different stages of
construction. Laboratory modeling (small scale and centrifuge) of reclamation process
using small clay lumps could achieve only limited success due to scale effects and also
cannot replicate the heterogeneity of the problem. One key and difficult to overcome
problem is the rapid softening of small clay lumps used in the laboratory experiments,
and also the contact stresses generated on small sized lumps for a given surcharge, are
higher than in the field (Tan, 2002). Therefore, in-situ evaluation is needed to
complement these small scale tests. A major site characterization program was carried
out as part of a research project. Field pilot tests are conducted in an ongoing
reclamation site at Pulau Tekong in Singapore to provide a basic understanding of the
state of lumpy fills at different stages during land reclamation works.
This chapter summarizes the results of an investigation from one such pilot
field test involving the use of dredged clay lumps and sand surcharge as fill materials
at this reclamation site. The Nuclear-Density cone penetration test (ND-CPT) is
employed to measure the continuous changes in density in addition to other usual cone
parameters. The ND-CPTs were conducted in two stages namely just after the lumpy
fill is formed prior to any soil treatment, and then after a sand cap has been placed on
top of the lumpy fill. A third stage is planned, but this will be after this thesis work,
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namely the state of the same fill after completion of consolidation with the aid of
vertical drain. However, for this final state, another site is used and this will be
reported in Chapter 6.
5.2 Site Description
The project site is located close to Changi in the northeastern part of Singapore
Island, as shown in Figure 5.1. The project site is approximately 5 nautical miles in the
longitudinal direction and 6.5 nautical miles in the latitudinal direction. Nautical charts
of the project area indicate wide ranging seabed elevations varying from 1.5m above
Chart Datum (CD) in the tidal flats and coastal shallows, to greater than 20m below the
Chart Datum (CD).
5.3 Geotechnical Characteristics of seabed soils
The economical and technical feasibility of any reclamation scheme will be
largely influenced by the availability of the fill materials and its characteristics. In part
of the project, dredged clay lumps obtained from excavations of seabed soils for the
construction of sand-keys and sand-bunds along the periphery of the land reclamation
project itself will be used back as fill. These subsoil conditions are important to decide
the dredging level for the construction of sand-keys and sand-bunds along the
periphery of the land reclamation projects. At the same time, the geotechnical
characteristics of seabed soils are needed before dredging to understand the nature and
behavior when they are dredged and used as fill. This is because it is difficult to
characterize the fill materials after dredging. Therefore, an extensive site investigation
was carried out as part of this project to investigate the geotechnical characteristics of
seabed soils. Marine boreholes, piezocone soundings, field vane shear tests and
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standard penetration tests were conducted around Pulau Tekong in the initial phase of
this mega reclamation project. However, all the data were collected by commercial
companies. A detailed characterization of Singapore marine clay at this site is also
given in Tan et al. (2002) and Low (2004). Thus as part of this thesis, the results from
the above site investigation will be used to review the geotechnical characteristics of
seabed soils in the following section.
5.3.1 Geological Profile
A desk study was first conducted on existing marine boreholes, which had been
carried out earlier by other parties and the geological profile of the underlying soil was
then derived. The preliminary site investigation and geophysical survey revealed that
the seabed soil at this site consists of four layers locally known as the surface soft
marine clay (SSMC) of recent deposits; upper marine clay (UMC), intermediate layer
(IML) and lower marine clay (LMC) followed by the residual soil or weathered
granite. A typical geological profile of the seabed soils at the project site is shown in
Figure 5.2. The borehole data revealed that the intermediate layer contains fragmented
shells and decomposed wood, which forms a heterogeneous layer. This intermediate
layer is now believed to be the desiccated top of the lower marine clay.
5.3.2 Physical Properties
The grain-size composition and index properties with depth are shown in
Figure 5.3. In the upper 4m of the sediment, the natural water content is greater than
the liquid limit, which results in a liquidity index greater than unity. Thus, the
sediment can be considered as a recent deposit lying on top of the upper marine clay
(UMC) layer and is given the name as surface soft marine clay (SSMC). Typically, the
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thickness of the upper marine clay layer which follows the SSMC varies from 8 m to
10 m. The range of index properties for different clay layers is similar to that of other
near shore areas in the territory of Singapore. The upper marine clay is usually very
soft with its natural water content in the range of 80 - 100 %. The liquid limit and
plastic limit are in the range of 80 - 110% and 30 - 60% respectively. Below this soft
upper marine clay layer is the intermediate heterogeneous layer, which is of medium
stiff-to-stiff clay layer of thickness of about 10-15m. The lower marine clay layer has
natural water content in the range of 50 – 60 %, liquid limit of 65 - 85 % and plastic
limit of 30 – 60 %. The Singapore marine clay also showed a wide range in swelling
potential, as shown in Figure 5.4(d).
5.3.3 Undrained Shear Strength Characteristics
Figure 5.4(a) shows the undrained shear strength profiles measured by
laboratory and field tests. Interpretation of the results indicates that a trend of
increasing undrained shear strength with increase in depth. The surface soft marine
clay (SSMC) is extremely soft and the upper marine clay (UMC) is usually very soft to
soft with its undrained shear strength between 10 to 30 kPa. Below this soft upper
marine clay layer is intermediate layer (IML), which is dense sandy silt or medium
stiff to stiff clay layer. This stiff intermediate clay layer is currently believed to be a
desiccated crust of the lower marine clay subjected to varying degree of weathering.
The other deposit, the LMC, is stiff to hard clay, with undrained shear strengths in the
range of 60 kPa – 100 kPa.
Lunne et al. (1997) suggested that the undrained shear strength can be
calculated from CPTU results from the following equation:
qt =su Nkt + σv (5.1)
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where qt is the corrected cone resistance, su is undrained strength, Nkt is the cone factor
and σv is the in-situ overburden total pressure. The cone factor was established by
comparing the undrained shear strength measured from UU tests and UCC test with
nearby CPTs from this project site and it showed that the range of values of the cone
factor, Nkt for seabed soils was found to vary between 8 and 12, with an average of
around 10, as shown in Figure 5.4(a). Studies carried out by Dobbie (1988) in
Singapore marine clay also showed that the Nkt ranged from 9 to 12 with an average of
about 10.5. Tanaka et al. (2001) also obtained the cone factor Nkt of 10 for Singapore
marine clay.
In addition, the properties of undrained remoulded strength were also
estimated. Wroth & Wood (1978) proposed the following unique relationship between
liquidity index and remoulded strength of soil.
Sur = 170 e-4.6LI (5.2)
where Sur is the remoulded undrained shear strength and LI is the liquidity index. The
remoulded strength represents the lower bound on undrained shear strength of the
material. Terzaghi (1944) has defined the sensitivity of clays as the ratio between the
undisturbed strength to remoulded strength at the same water content and therefore, it
is a measure of strength upon disturbance. The sensitivity of the seabed soils is
estimated and shown in Figure 5.4(b). Based on the sensitivity classification suggested
by Skempton and Northey (1952), the Singapore marine clay can be considered as
medium sensitive to sensitive clay. From the dredging point of view, the remoulding
loss is important and estimated, as shown in Figure 5.4(c). The remoulding loss of the
seabed of soils is about 80-90% at shallow depths and reduces to about 60 – 70% at
deeper depths. The soil structure of the seabed clay that has originally developed at the
seabed may be disturbed in the dredging and transporting processes. The state of the
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seabed soils immediately after dredging needs to be examined and discussed in the
subsequent section.
5.3.4 Consolidation Characteristics
The variations of the preconsolidation pressure and OCR profiles with depth
are shown in Figure 5.5(a) and (b). The value of preconsolidation pressure was
determined from the oedometer test results using Casagrande procedure (Casagrande,
1936). A line representing the present vertical effective stress is also shown in Figure
5.5(a). As can be seen in Figure 5.5(b), the OCR is relatively high near the seabed, and
is seen to decrease with depth approximately from between 2 and 6 just beneath the
seabed to between 2 and 3 at the end of the lower marine clay. The upper marine clay
was moderately to heavily overconsolidated with an overconsolidation ratio (OCR) of
2 to 6, the lower marine clay were lightly overconsolidated, with an OCR of 2 to 3.
The variation of compression index and swelling index with depth are also shown in
Figure 5.5(c) and (d).
5.4 State of Fill Materials after Dredging
Engineering properties of dredged material vary not only by in-situ geographic
location but also with type of dredger used. The type of dredger used will be dictated
primarily by the properties and quantities of geotechnical materials to be excavated
(Leussen et al. 1984), although other factors such as dredger availability and
production rate, dredging and disposal site locations and conditions also matter.
Poindexter-Rollings (1994) have also reported the sediment type and conditions
associated with dredger type and its variations in the dredged material volume over
time for selected sediments that were hydraulically dredged. Katagiri et al. (2000)
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studied the change of geotechnical characteristics of clay lumps from dredging to
reclamation. They also found that the degree of disturbance of dredged clay lumps
depends on the dredging procedure and original properties of the deposit. Bo et al.
(2001) also compared the geotechnical characteristics of dredged materials at a borrow
area and after placement of dredged materials in a reclamation pond. They reported
that the geotechnical properties of dredged big clay lumps do not change very much
due to dredging, transportation and dumping.
In the present project reported in this thesis, the seabed is dredged using very
large clam-shell grab, with capacity ranging from 4m3 to 25m3. The seabed soils are
disturbed during dredging, but the degree of disturbance depends on the state of
original soil properties and dredging procedures. The geotechnical properties obtained
from the site investigation revealed that the surface soft marine clay (SSMC) layer is a
very soft and recent deposit. Visual observations made during the dredging process of
the SSMC revealed that the weak structure of the soil that had developed over time
was completely destroyed by the dredging procedure and existed in the form of slurry
after dredging. At some places, where the dredging of SSMC produced big soft clay
lumps, these lumps deformed completely during subsequent dumping with other
dredged materials in the barge, as shown in Figure 5.6(a). When these dredged
materials are dumped into a reclamation pond, their water content increases largely due
to mixing with water and some degree of particulate segregation also occur in the
disposal pond.
On the other hand, UMC is generally soft, IML is medium stiff to stiff and
highly heterogeneous and LMC is medium stiff. After dredging, UMC and LMC exist
in the form of clay lumps while for the case of IML, if the sand and silt contents are
high then lumps could not be formed. Typical state of the clay lumps obtained from
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UMC, IML and LMC immediately after dredging is shown in Figures 5.6(b), (c) and
(d). The dredging of these materials produces stiff clay lumps of varying size and
shapes but in general, these lumps are usually quite big (1m3 – 8m3 in volume), as
shown in Figures 5.6 (b), (c) and (d). At the same time, these dredged clay lumps when
placed in the reclamation pond, will undergo three-dimensional swelling due to high
suction developed when dredged and the subsequent availability of seawater all around
(Robinson et al. 2004). However, it is still not understood how the geotechnical
characteristics of these stiff clay lumps will change after dumping in the reclamation
pond. The in-situ state of these dumped dredged materials needs to be evaluated and is
discussed in the subsequent sections.
5.5 Method of Reclamation using big clay lumps
As stated earlier, large dredged clay lumps of up to 8m3 in volume were
excavated along the periphery of the reclamation pond using clam-shell grab. A typical
clay lump dredged from the seabed was shown earlier in Figure 1.5. These dredged
clay lumps were placed in bottom-opening barges, as shown in Figure 1.6 and
transported to a reclaimed site, where the lumps were discharged on to the seabed, as
shown in Figure 5.7. After the lumps had been dumped to a desired depth (-3mCD),
usually limited by the draught of the vessels used for transportation, sand was used to
cap the dredged clay lumpy fills, and also for subsequent filling above the sea level to
provide the surcharge to accelerate settlement. The capping sand was placed in several
lifts up to + 4mCD.
Figure 5.8 shows a schematic section of the reclamation site with dredged clay
lumps and sand surcharge. During initial stages of reclamation, there would be large
voids between the big dredged clay lumps and these inter-lump voids (void between
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lumps) could be partly filled with water / or slurry and small clay lumps. As a result of
consolidation and compression from the sand surcharge, average density and void ratio
of lumpy fills constructed using dredged clay lumps change continuously. If the inter-
lump voids (void between lumps) reduce to the size of intra-lump voids (void within
the lumps), then the lumpy fill is considered to have been “homogenized” that is, no
more inter-lump structure. From a construction perspective, the initial state of the
lumpy fill needs to be established before a contract can be called for the topping up.
Subsequently, the change in the state of the ground in particular the final state also
needs to be ascertained. This is clearly a major challenge and the results presented here
is a first step towards achieving this understanding.
5.6 In-Situ Evaluation of Initial State of Lumpy Fill
As part of the Pulau Tekong project carried out by the Housing and
Development Board (SURBANA), 3 field pilot test areas were created, TA 1, TA 2,
and TA 3 as shown earlier in Figure 5.1. In the following section, the results of an
investigation from one such pilot field test involving the use of dredged clay lumps and
sand surcharge as fill materials will be discussed.
5.6.1 Site Investigation Scope
A ND-CPT was used in a series of site investigations to evaluate the state of
the lumpy fill at two different stages. The first stage is immediately after placing the
dredged materials in the reclamation area up to -3 mCD (Stage 1) and the second stage
is immediately after dumping the capping sand, up to +4 mCD (Stage 2). A third stage
is also planned and this will be after the end of consolidation and is going to be after
the completion of this thesis work.
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In Stage 1, as the surface of the fill is below sea level, ND-CPTs were carried
out using a Marine Cone Penetration System as shown in Figure 5.9. The control unit
and the hydraulic power unit were placed on the barge. A hydraulic penetration
system, which was mounted on seabed rig or steel frame/ tower, was lowered on to the
surface. The reaction force was provided by the dead weight of the steel tower. The
barge is equipped with a four-point anchor mooring system to secure the barge in
position and to maintain its stability during operations. In Stage 2, land is already
formed above the sea level using sand to cap the lumpy fill and a conventional CPT
crawler was used to carry out the ND-CPTs, as shown in Figure 5.10.
5.6.2 Field Investigation Layout
In this study, the results of an investigation from a field pilot test (TA 2) will be
discussed in greater detail. This is one of 3 planned field pilot test areas involving the
use of dredged clay lumps and sand surcharge as fill materials. The pilot test area (TA
2) is 100m long and 100m wide. The clay lumps were placed directly on the seabed
which is about -13 to -14mCD from bottom-opening barges to form an 8m to 9m thick
lumpy fill layer from June to July 2002. A total of 120 numbers of marine ND-CPTs
were conducted from August to November 2002 (Stage 1). Subsequently, 7m of sand
was placed in several lifts up to +4mCD over a period of 10 months. 120 numbers of
ND-CPTs were conducted at the same locations as in Stage 1 from December 2003 to
May 2004 (Stage 2). The Stage 2 ND-CPTs were established in accordance with the
built–up coordinates of Stage 1. However, it is impossible to make sure that the ND-
CPT is carried out in exactly the same locations as in Stage 1, because of all inevitable
surveying setting-out error of about ± 0.5m. While such a small deviation usually does
not pose any problem in a site investigation, in a lumpy fill, this could be a problem.
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The investigation plan carried out at TA 2 for Stage 1 and Stage 2 is shown in
Figure 5.11, which consists of a big grid and a small dense grid. The big grid is 99m x
100m and the small grid is 10m x 11m. The small dense grid is located at the centre of
the big grid, which is highlighted in Figure 5.11 as ‘A’. The big grid consists of 110
ND-CPTs and the small dense grid has 10 ND-CPTs, which are very closely spaced, as
shown in Figure 5.11. The present test arrangement was designed specially to provide
adequate information to characterize a representative volume of lumpy fill and also
sufficient idea of the variation.
5.6.3 Need of ND-CPT in Characterization of a Lumpy Fill
As discussed previously, when the dredged clay lumps were used for land
reclamation, initially, there would be large voids between the big dredged clay lumps
and these inter-lump voids could partly be filled with small lumps and / or water. Now,
when the cone penetrates into this complicated soil, a number of probable soil profiles
can result. Typical cone resistance, pore pressure and wet density profiles obtained
using ND-CPTs at locations RI 111B, RI 104, RI 13 and 101B are shown in Figures
5.12 to 5.15. The changes in wet density, cone resistance and pore pressure together
can be employed to identify the various sizes of clay lumps and inter-lump voids, as
shown with horizontal lines in Figures 5.12 to 5.15. These figures show that there are
appreciable changes in properties, confirming the heterogeneity of a lumpy fill. From
the density profile in Figure 5.12, two significant spikes could be observed at -7mCD
and -11mCD. However, cone resistance and pore pressure profiles shows that there is
only one spike at -7mCD. As concluded previously in Chapter 4, in a ND-CPT, the
maximum radius of the influence zone or measuring sphere about the radioactive
source is about 23.6 cm radius, and thus the density measured reflects the average
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around the central point of the radioactive source and detector configuration, in
contrast with the essentially point-wise measurement in cone resistance and pore
pressure. Thus Figure 5.12 suggests that this particular ND-CPT penetrates near to the
edge of a clay lump from -8mCD to -12mCD, this is distinguished by the high average
wet density and very low cone resistance. However, from -6mCD to -7mCD, it is
penetrating into the interior of a clay lump, thereby measuring a high wet density and
very high cone resistance at this depth. This vividly shows that using the cone
resistance and pore pressure alone would have not picked up this detail.
At the same time, if there is no density measurement, then it is possible to infer
from the usual cone parameter profiles that at this depth, the cone has penetrated only
soft slurry in the void and this will mislead the interpretation of the actual ground.
Similar observation could also be made in Figure 5.13 and 5.14. The wet density, cone
resistance and pore pressure profiles measured by ND-CPTs at these locations are
quite similar to the profile described earlier. Figure 5.15 shows typical results obtained
by the ND-CPT at location RI 101B. This figure shows that there are significant spikes
indicating the presence of lumps, as reflected by the combination of density and usual
cone parameters. Therefore, for a highly heterogeneous lumpy fill site, the addition of
one more parameter, the wet density, helps tremendously in the interpretation of
results.
5.7 Problems related in marine based investigation (Stage 1)
Problems in marine based ND-CPT investigation comes mainly from the fact
that the current design of the ND-CPT requires two probings for each measuring point,
to obtain first the background count due to naturally occurring gamma photons, and
then to measure the actual nuclear density (RI) count, so as to obtain the gamma-ray
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emitting from the gamma-source and scattered in the soil medium. The background
count is measured using a dummy cone, in which only the detector is placed to
measure the naturally occurring gamma photons. As already discussed in Chapter 4,
the intensity of background count measured at a point varies greatly depending on soil
type, mineral makeup, density of materials and its geological history. In a rough way,
these profiles could possibly be used for a very preliminary classification of the soil
type when other more decisive information is not available.
Figure 5.16 shows typical background count profiles obtained for
homogeneous soils in Japan. It can be seen in these background count profiles that
there are little fluctuations with depth. Hence, if the soil is homogeneous and the
variation in the background count profile is negligible within a test site, then double
probing is not required for every single measuring point. Instead, only the RI count
needs to be measured at each point and an average background count within the test
site is then used to determine the wet density of soil. This is especially useful in marine
measurement where every probing is time consuming, and there will be great saving in
cost if the total number of probings can be reduced.
Figure 5.17 shows typical RI and background count profiles obtained for the
lumpy fill site at locations RI 45, RI 111, RI 115, RI 116, RI 118 and RI 120, which
are in the small dense grid, shown in Figure 5.11. Although all the six ND-CPTs are
very closely spaced within a 5.0m x 5.5m square grid, significant variation in RI and
background count profiles can still be observed, suggesting that the lumpy fill is highly
heterogeneous. With this degree of variation in the background count, the use of an
average background count profile within the test site needs to be examined. Figure
5.17(b) also shows an average background count profile obtained for the above six
profiles. If an average background count profile is used to determine the wet density,
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then, an error of about 10% is observed in the estimated wet density as shown in
Figure 5.18 for locations RI 45 and RI 115. Therefore, for highly heterogeneous lumpy
fill sites, two probings are required at every single measuring point.
But in a marine based investigation (Stage 1), it is very difficult to ensure that
the two probes are pushed through exactly the same hole due to operational difficulties
unless divers are used, which is economically not viable. The variation in built-in
coordinates for the two different probings is about 0.15m to 1.5m. The non-
correspondence of data obtained with two different holes will affect the accuracy of the
measured density for the highly heterogeneous lumpy fill site. To avoid this
discrepancy in the measured density profile, it is desirable to measure both the RI and
background count with one probing. The detailed description of the development of a
single probe Nuclear-Density Cone penetrometer will be discussed in detail in the
following section.
5.7 Improvements in Nuclear-Density Cone Penetrometer for marine
based investigation
To support the ongoing engineering works, the above issues need to be
addressed urgently. Towards this purpose, a new single probe Nuclear-Density Cone
Penetrometer is developed by modifying the double probe where the gamma-ray
section is extended so as to insert an additional detector that is outside of the gamma-
ray zone emitting from the source. With this, the cone is able to measure both the
background and actual RI count during the same probing, thus removing the need to do
two probings.
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5.8.1 Description of Single Probe ND-CPT
Figure 5.19 shows major components of the Single Probe Nuclear-Density
Cone Penetrometer (ND-CPT). The lower part of the new cone is similar to the old
ND-CPT where it houses various sensors to measure the usual cone parameters,
namely, cone resistance (qc), pore pressure (u2), and the sleeve friction (fs). The upper
part of the cone section is extended so as to insert an additional detector to measure the
naturally occurring gamma photons. This upper part houses the Radioisotope source,
and two detectors. The detector-1 is used to measure the actual nuclear density (RI)
count and the detector-2 is used to obtain the background count of naturally occurring
gamma photons.
Depth Corrections
As already mentioned in Chapter 3, the original measured cone data needs to be
corrected for depth corrections to determine the actual wet density of material.
Therefore, depth adjustment needs to be carried out on measured data from the Single
Probe ND-CPT. If the measurement center for the cone is considered at the cone
resistance sensor, then the other sensors readings are adjusted accordingly. The depth
corrections for pore pressure (0.04m), sleeve friction (0.11m) and RI Count (0.60m)
remain the same as in the old ND-CPT while the BG Count data needs to be shifted up
by about 1.201m.
Detector Efficiency Ratio
As described earlier, in the single probe ND-CPT, two detectors were housed to
measure both the actual nuclear density (RI) count and the background (BG) count of
naturally occurring gamma photons, whereas, in the double probe ND-CPT, the RI
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count and BG count are measured by the same detector but in two separate probing.
The material used in the construction of the new additional detector (detector-2) in this
new cone is not the same as that of the old detector (Detector-1). Hence, the counting
efficiency (numbers of counts recorded per unit time) of these two detectors are not
similar and it was found that the detector efficiency ratio between Detector-1 and
Detector-2 is 1.0353. Therefore, it is necessary to employ a detector efficiency ratio
while calculating the effective gamma count for the single probe ND-CPT. The
effective gamma count is calculated by multiplying the BG count by the detector
efficiency ratio (1.0353) and this value is then subtracted from RI count.
5.8.2 Comparison of Single and Double Probe ND-CPT
As discussed previously, in a marine based investigation, it is impractical to
ensure that the two probes can be pushed into an identical hole. Therefore, the
comparison of the double and single probe ND-CPT was carried out when land is
formed above the sea level. Out of a total of 120 tests in Stage 2, 10 tests were used
for this purpose. The locations are 19C, 28C, 33C 36C, 40C, 65C, 71C, 91C, 109C and
121C in Figure 5.11. 10 numbers of double probe ND-CPTs were conducted from 4th
December to 12th December 2003. Unfortunately, the single probe ND-CPT could not
perform immediately after completing the double probe due to some practical
problems encountered. The problems arose mainly because of an increase in the length
of the single probe ND-CPT due to the need to insert an additional detector. When this
new long cone was initially used, the cone was damaged as a result of bending due to
the presence of a dense sandy layer above the ground-water table and it takes about a
month to modify the new cone structure. To avoid damages to the equipment, the pilot
test hole was drilled about 6m from the ground level for the remaining ND-CPT
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locations in Stage 2. The loss of information for the first 6m of the sandy layer is not
critical to this study. The single probe ND-CPTs using a new cone were conducted in
the same hole from 5th January 2004 to 15th January 2004. As this was carried out one
month after the double probe test, during this time, some additional settlement was
observed in the newly reclaimed land. The settlement was measured and adjusted in
the measured wet density profiles accordingly.
The wet density profiles obtained from the double probe ND-CPT are
compared with the single probe ND-CPT and the results using the same calibration
chart show a very good agreement, as shown in Figure 5.20. The results from only four
out of the 10 ND-CPTs are shown in Figure 5.20 for illustration. This also means that
the separation distance between the two detectors is sufficient, so that Detector-2 is
able to measure the background count accurately. It can be also seen that there is a
very good agreement in the measured wet density profiles for both the sand fill at the
top and the soft clayey seabed at the bottom. However, there are some small
differences in the spikes between the single probe and double probe for the highly
heterogeneous lumpy fill in between the sand and seabed. The small variation in wet
density spikes may be attributed to the average measurement of ND-CPT within the
measuring volume. As explained earlier, the cone measures density over a radius of
23.6 cm, therefore results from the cone tend to be average values rather than spot
values. In addition, these measurements are averaged over a span of 10cm depth to
minimize the statistical fluctuations. In spite of these small differences, it is clear that
the single probe ND-CPT has performed very well in measuring the wet density
profiles.
One of the main advantages of this newly developed Single Probe ND-CPT is
that it eliminates the need for double probing and the uncertainties that are involved in
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the investigation of a highly heterogeneous profile as result of the inability to carry out
both probings in an identical hole. The use of a single probe device in a marine
investigation is a significant improvement in the design.
5.9 Characterization of Initial State of a Lumpy Fill
As shown schematically in Figure 5.8, a lumpy fill layer of about 8m thickness
was constructed using big clay lumps. On top of this, 8m thick sand layer, which acts
as a surcharge to accelerate the consolidation of the clay lumps, was placed. The ND-
CPT was extensively used to evaluate the in-situ initial state of the fill formed by the
dredged clay lumps. The test has been conducted on a recently formed lumpy fill prior
to placement of the sand fill (Stage 1) and after a sand cap has been provided (Stage 2).
The initial state of the reclaimed land will be described in the following paragraphs
using two typical profiles obtained using the ND-CPT.
Figures 5.21 and 5.22 shows typical cone resistance, pore pressure and wet
density profiles obtained at pilot test area (TA 2) in Stage 1 and Stage 2 at locations RI
91 and RI 71. The changes in wet density, cone resistance and pore pressure together
can be employed to identify the various interfaces between soils layers, as shown by
the horizontal lines in Figure 5.21 and 5.22. The pore pressure response suggests that
the water table was about 2.5m below the ground level. The cone resistance was quite
high near the ground-water table as a result of compaction brought about by flow of
water in the fill carrying away finer material from the sand mixture and the possible
over-consolidation effect due to the downward seepage flow. The sand density above
the ground water table was also increased due to mechanical compaction as a result of
leveling operations by bulldozers. By comparing the cone resistance, pore pressure
and wet density profiles in Stage 2, it is clear that the sand fill which is above -7.0
136
mCD and the seabed clay which is below -14 mCD are homogeneous, but the lumpy
fill in between these two is heterogeneous. This is also clearly observed in the Qt
versus Bq chart (Robertson, 1990), as shown in Figure 5.23.
It is also observed that there is no clean sand pocket found in the lumpy fill, an
indication that the sand used to cap the lumpy fill could not replace the materials in the
large inter-lump voids. This is attributed to the construction method used to place very
soft clay materials on top of the dredged clay lumpy fills prior to placement of the sand
capping. This was to facilitate the trimming of the clay fill to exactly -3 mCD as
stipulated in the contract. This very soft clay material is believed to have filled into the
large initial inter-lump voids present in the lumpy fill layer. Hence, the sand used to
cap the lumpy fill could no longer penetrate the slurry in the inter-lump voids. This
argument is supported by the pore pressure response within the lumpy fill layer at
Stage 2 (Figure 5.21 and 5.22). The average pore pressure increase over the entire
thickness of lumpy fill is almost identical with that measured in homogeneous seabed
and consistent with the initial increase in pore pressure, as expected in one-
dimensional consolidation from 8m of sand surcharge. The initial state of lumpy fill
layer will be discussed in detail in the following section.
5.10 Initial State of Lumpy Fill Layer
There are two important issues on the initial state of lumpy fill layer that need
to be evaluated: (i) whether the inter-lump voids are filled with slurry or water and (ii)
the state of dredged clay lumps at various stages. These issues are explored with the
help of the ND-CPT results.
Figure 5.24 shows enlarged wet density profiles within the lumpy fill layer at
RI 91, RI 71 and RI 36 during Stage 1 and Stage 2. As demonstrated previously in
137
Chapter 4, from the back analysis of the field measurement using the theoretical
models, the size of clay lumps and inter-lump voids can be identified. In Figure 5.24
(a), two significant density spikes could be observed, and the depth between these
peaks is an indirect indicator of the size of the inter-lump voids. It can be also deduced
that the clay lump sizes are about 1m to 2m, consistent with that shown in Figure 1.6.
Also, in the inter-lump voids, the density is relatively high, generally about 14 kN/m3.
This confirms that the voids have not been filled with sea-water, but with slurry. This
is consistent with the observation that the seabed is covered with a very soft marine
clay, with wet density of about 14 kN/m3 or water content of 110%, as shown in Figure
5.3. While comparing the wet density profiles in Stage 1 and Stage 2 in Figure 5.24
(a), upon the application of sand surcharge, there are large vertical and horizontal
movements taking place in the lumpy fill layer. This is due to the nature of the fill
which consists of large clay lumps and inter-lump voids filled with clay slurry.
Similar observations could be also made in Figure 5.24 (b) and (c). In Figure 5.24 (b),
during Stage 2, there is a decrease in wet density of the lumpy fill layer from -7mCD
to -10mCD and this may be attributed to the softening of clay lumps, which is
explained in a subsequent section.
5.11 Intrinsic and Intact Compression Curves
The compressibility characteristics of reconstituted clays are used as a valuable
frame of reference for assessing the properties of an intact natural material (Burland
1990). The properties of the reconstituted clay are termed as ‘intrinsic’ since they are
inherent to the soil and independent of the natural state. The intrinsic compression line
(ICL) is a valuable reference line for studying the compression characteristics of
natural clays. Burland (1990) introduced a normalizing parameter called the ‘void
138
index’ to aid in correlating the compression characteristics of various undisturbed soil
samples. The void index (Iv) is defined as
Iv = *
*100
*1000
*100
*100
cCee
eeee −
=−
− (5.3)
where e is in-situ void ratio; e*100 and e*1000 are the intrinsic void ratios on the ICL
corresponding to σv′ = 100 kPa and σv′=1000 kPa respectively. C*c is the intrinsic
compression index which is defined as (e*100 – e*1000). Burland (1990) showed that the
intrinsic compression curve from soils within a wide range of liquid limits, when
plotted in terms of void index, could be represented with sufficient accuracy by the
following equation:
Iv = 2.45 – 1.285 X + 0.015 X3 (5.4)
where X = log σv′and σv′ is in kPa. The values of e*100 and C*c are measured by
means of an oedometer test on the reconstituted soil. Burland (1990) also showed that
e*100 and C*c could be reasonably related to the void ratio at the liquid limit, eL, as
follows:
e*100 = 0.109 + 0.679eL - 0.089eL
2 + 0.016eL3 (5.5)
C*c = 0.256eL – 0.04 (5.6) Low (2004) found that for reconstituted Singapore marine clay, Eq. (5.4) to Eq. (5.6)
were also applicable. Therefore, this framework will be used to study the compression
characteristics of the lumpy fill layer. As part of this thesis, this author has already
demonstrated that the ICL and void index from oedometer tests can be used in the
study of the compression characteristics of the ultimate state of a reclaimed land
(Karthikeyan et al. 2004).
139
As the ND-CPT provides a continuous profile of wet density, it can be used to
calculate the in-situ void ratio of the soil. The effective vertical pressure can be
estimated from total vertical stress and the pore water pressure. However, the pore
water pressure is assumed to be hydrostatic. Hence, the in-situ void ratio versus
effective vertical pressure relation can be obtained from the ND-CPT results. Burland
(1990) intrinsic framework is then used to interpret this relation. As a first step, the
result from pilot test area TA 1 shown earlier in Figure 5.1 is discussed. In this pilot
test area, limited numbers of ND-CPTs were carried out in the seabed clay prior to the
dumping of dredged materials. Figure 5.25 shows the typical cone resistance, pore
pressure, and wet density profiles obtained from ND-CPTs in the seabed clay. The wet
density profiles show here are consistent with the soil layers shown in Figure 5.3. The
results obtained from the ND-CPT, as shown in Figure 5.25 are re-plotted in terms
void ratio (e) and effective vertical pressure (σv′) and shown in Figure 5.26.
Figure 5.26 shows typical e-log σv′ curves obtained from interpretation of the
ND-CPT results. The results show that marked scatter in the e-log σv′ curves which is
due to variations in depositional conditions as the different layers of soil profiles were
being formed. The depositional environments differ significantly as a result of sea
level changes and changes in the course of the river. There is no reason to anticipate a
set of smooth compression curves. Rates and modes of deposition are likely to vary
considerably during the formation of a sedimentary soil layers and in these
circumstances a wavy curve must be expected (Edge and Sills, 1989). The e-log σv′
curves obtained from ND-CPT results will be examined using Burland (1990) intrinsic
framework to capture the compressibility characteristics of natural deposits in the
following paragraphs.
140
Figure 5.27 shows ve σ ′− log compression and swelling curves obtained from
oedometer tests on reconstituted soil samples from this area. The reconstituted soil
samples were prepared with the water content of 1.5 times the liquid limit. The
compression data in Figure 5.27 are re-plotted in Figure 5.28 by replacing void ratio
(e) with the parameter void index (Iv). When plotted in terms of void index (Iv), the
data indeed fall on to a unique ICL curve, as reported by Burland (1990). The ICL
proposed by Burland (1990) as given by Eq. (5.4) is also plotted in Figure 5.28 and it
can be seen that this indeed is appropriate for the soils tested here.
Intact compression curves obtained from the ND-CPT, as shown in Figure 5.26
are plotted in terms of Iv and compared with the ICL and shown in Figure 5.29. The
two mechanical properties (e*100 and C*c) were determined from one-dimensional
compression tests on reconstituted soil samples. These parameters were used to
compute void index using Eq. (5.3). Burland (1990) found that many low to medium
sensitivity natural clays that are deposited in still water environment lie close to a well
defined line to the right of the ICL which is defined as the Sedimentation Compression
Line (SCL) and this is also shown in Figure 5.29. The location of the intact
compression curves relative to the ICL and SCL reflects the depositional and post-
depositional history of the deposit. This figure shows that the intact compression
curves for the upper part of the seabed clay lies on or close to SCL while the lower part
lies below the ICL. If an intact compression curve lies on or close to ICL, the in-situ
state of the sample is normally consolidated (NC). Similarly, if an intact compression
curve lies below the ICL, the state of the sample is overconsolidated (OC). The data
obtained from ND-CPT clearly indicate that the upper 4m of the sediment is a recent
deposit of surface soft marine clay and is normally consolidated. However, the other
deposits are over consolidated clays. These observations are consistent with the
141
consolidation characteristics of seabed soils given in Tan et al. (2002) which had
indicated that the upper marine clay below the surface soft marine clay is
overconsolidated. The results above show that the ND-CPT is very useful to provide
the kind of results needed to use the intrinsic frameworks proposed by Burland (1990)
to capture the compressibility characteristics of the natural deposit. Hence, this
framework will now be used to describe the qualitative nature of the initial state of a
lumpy fill.
The measurements from ND-CPTs for the lumpy fill layer are now used to
obtain the intact compression curves, which are plotted in terms of Iv and compared
with ICL and SCL, as shown in Figure 5.30 and 5.31. These figures clearly show that
certain zones of the compression curves lie above ICL and close to SCL, which is
similar to the recent natural deposit of the surface soft marine clay, as shown in Figure
5.29 and other zones that are overconsolidated. The intact compression curves
resulting from the placement of sand surcharge are very much steeper than the ICL and
it is clear that these curves will drop below the SCL at higher values of effective
overburden pressure. These data clearly indicate that the lumpy fill layer has both
consolidating and overconsolidated zones. The formation of this lumpy fill layer will
be described in the subsequent section.
5.12 Radioisotope (RI) Cone based assessment
The void index (Iv) may be used as a measure of intrinsic compactness of soil
(Burland 1990). When the void index (Iv) is less than zero the soil is “compact” and
when it is greater than zero the soil is “loose”. The term “loose” was used by Burland
(1990); however the term “loose” may lead to confusion when used for clayey soils.
The term “loose” hitherto will be referred as “less compact”. The void indices versus
142
depth profiles at three typical locations are shown in Figure 5.32. The density
measured by the ND-CPT was used to calculate the in-situ void ratio. These values
were used to compute void index, as given by Eq. (5.3). As can be seen, compact and
less compact zones exist within the lumpy fill layer.
5.13 Softening of Clay Lumps and Remoulded Shear Strength
Because of the removal of overburden stresses during dredging operations,
suction equivalent to the mean overburden pressure would develop in the clay lumps.
When these clay lumps are dumped in seawater during the land reclamation process,
they will absorb water because of the suction present in the soil. Subsequently, the
suction reduces with time and the water content increases resulting in a decrease in the
strength of the clay lumps. (Robinson et al. 2004). However, the degree of softening of
these stiff clay lumps after dumping in the reclamation pond has not been established
to date.
If the clay lumps swell and soften in the reclamation pond, the state of clay
lumps may collapse and remoulding/ or re-consolidation took place after the placement
of a sand surcharge. Therefore, the remoulded shear strength of these dumped dredged
materials needs to be evaluated. Houston and Mitchell (1969) suggested the existence
of a unique relation between liquidity index and remoulded undrained shear strength of
clays. Wroth and Wood (1978) proposed the relationship between liquidity index and
remoulded shear strength of clays, as given by Eq. (5.2). Kulhawy and Mayne (1990)
reported that the Wroth and Wood (1978) equation shows good agreement with
measured data in the range of 10 kPa to 300 kPa. For soil samples with natural water
contents close to the liquid limit, the estimate of the (very low) remoulded strength
may be misleading, but these will be the soil deposits that tend to be sensitive, and for
143
which the estimates of the remoulded shear strength would be inappropriate anyway.
However, for overconsolidated clays, having natural water contents closer to the
plastic limit, there is usually little sensitivity and the remoulded strength should form a
lower bound to the in-situ strength. To examine the in-situ state of clay lumps, the
remoulded shear strength of the lumpy fill layer was estimated.
The specific gravity for clay particles in Singapore marine clays varies from 2.6
to 2.7, but in the present calculation, an average specific gravity of 2.65 was assumed.
The wet density measured by ND-CPT is then used to calculate the in-situ water
content. As discussed previously, the liquid limit and plastic limit of Singapore marine
clays varies from 80 – 100 % and 30 - 40% respectively (Tan et al. 2002), as shown in
Figure 5.2. In the present calculation of the liquidity index, however, an average liquid
limit of 90% and plastic limit of 35% were used. These parameters were used to
compute the remoulded undrained shear strength, as given by Eq. (5.2). The variation
of the estimated profile of remoulded undrained shear strength of lumpy fill layer with
depth is shown in Figure 5.33. In Stage 2, there is a slight increase / or decrease in the
shear strength of the material in the inter-lump voids and this may be due to the re-
consolidation/ or remoulding of the clay lumps after the placement of sand surcharge.
As confirmed earlier, the inter-lump voids have not been filled with seawater, but with
slurry of a significantly higher density than seawater. Hence, the strength is relatively
low in the inter-lump voids and this water content is greater than the liquid limit of the
in-situ seabed marine clay. But the key issue here is that the material in the inter-lump
voids is soil-like, exhibiting some shearing resistance, rather than behaving like a fluid.
As can be seen in Figure 5.33, the remoulded undrained shear strength of the clay
lumps is almost close to the lower bound of the in-situ undrained shear strength
developed at the original seabed clays and it is clearly indicating that the big clay
144
lumps have not softened completely. The initial pore pressure in all the clay lumps
excavated is negative, and thus this will swell once in contact with seawater after being
dumped.
To support these evaluations, as part of this reclamation project, co-researchers
Robinson et al. (2004) conducted a series of three-dimensional swelling tests using big
clay lumps when different diameters of clay lump specimens were fully submerged
underwater. Here, 105mm and 205mm diameter clay lumps were used. The
dissipations of suction at the centre of these samples were also measured. More details
about these experimental investigations can be found in Robinson et al. (2004). Figure
5.34 shows the photographs of 205 mm diameter Singapore marine clay lump before
and after three-dimensional swelling. It was found that the state of the clay lumps were
stable at the end of the dissipation of suction, as can be seen in Figure 5.34. The
variations of water content with depth of the sample at three different locations were
also measured, as shown in Figure 5.35. This figure shows that the measured water
content at the end of the test is not uniform along the diameter of the specimen. The
water content at the edge of the clay lump is higher than that at the centre, a fact of
some practical relevance. During the deformation process of the clay lumps in a lumpy
fill under sand surcharge, the edges of the clay lumps experience very high contact
stress and will cause partial disintegration of edges of the bigger clay lumps while the
centre of these lumps remains close to its original consolidated state.
5.14 Formation of initial state of lumpy fill layer
The measured engineering properties of the lumpy fill layer are now used to
reconstruct the formation of the layer. An explanation for the existence of
consolidating and overconsolidated zones is as follows. The significant variation in
145
soil properties within the lumpy fill layer indicates the complex interaction between
clay lumps that have not softened completely and the new infillings comprising mainly
of the slurry clay and also smaller lumps from the lumpy clays disposed at the site. The
initial pore pressure in all the lumps excavated is negative, and thus it will swell once
in contact with seawater after being dumped. This swelling as well as the high contact
forces between lumps will cause disintegration of the smaller lumps and partial
disintegration of edges of bigger clay lumps while the centre of these lumps remains
close to its original consolidated state. These small breakaway lumps will also fill the
inter-lumps voids. The lumpy fill layer, after the placement of a sand surcharge, has
consolidating and overconsolidated zones, in which the overconsolidated zone is
consistent with that of the original clay lump while the consolidating zone is due to the
infilling of inter- lump voids with very soft clay slurry and also breakaway little lumps.
This observation has important practical ramifications because it implies that the inter-
lump voids are filled with pockets of very soft clay and therefore unlikely to have such
voids still opened to cause long term settlement. It also means that these pockets of
very soft clay can be treated using vertical drains and sand surcharge, a soil
improvement that is needed anyway to treat the thick deposits of soft seabed clay
below the reclaimed area.
Figure 5.36 shows a histogram of frequency of in-situ void ratio measured by
the ND-CPT for lumpy fill layer in Stage 1 and Stage 2. All ND-CPT measurements
are captured in Figure 5.36 to provide sufficient data for more meaningful statistical
analysis. The average in-situ void ratio within the lumpy fill layer in Stage 1 is about
2.18. As expected, it has been reduced to 2.09 upon the application of sand surcharge.
With this, it can be calculated that about 5% of inter-lump voids have been closed after
the placement of sand surcharge.
146
Due to subsequent consolidation, the excess pore pressure in the lumpy fill
layer will dissipate and it results in further reduction of both inter-lump and intra-lump
voids (voids within lumps). At the ultimate state, if the size of the inter-lump voids
reduces to size of the intra-lump voids, then it is considered that the lumpy fill has
been “homogenized”. However, it is not clear whether the lumpy fills constructed
using such clay lumps indeed “homogenize” after fully consolidated. This issue needs
to be examined so that the large dredged clay lumps can be used as fill materials for
land reclamation with increased confidence. Therefore, a case study on the ultimate
state of a reclaimed land using big clay lumps has been carried out. For this ultimate
state of a reclaimed land, another site is used and this will be discussed in next chapter.
5.15 Concluding Remarks
A comprehensive site investigation was carried out at a reclamation site where
dredged clay lumps are used as fill materials. The investigations have been conducted
in two stages, one just after the lumpy fill is formed prior to placement of capping
layer any, and the second after a sand cap has been placed on top of the lumpy fill. The
ND-CPT was extensively used to evaluate the in-situ initial state of the fill formed by
these dredged clay lumps. Results from these tests show that usual cone parameters
coupled with the additional density measurement will provide a much more complete
picture of the fill formed. Problems faced while performing ND-CPTs in marine based
investigation were also highlighted and this has led to the development of a new single
probe ND-CPT. The comparison of the wet density measured by the double probing
ND-CPT with the single probe ND-CPT measurements showed very good agreement.
The density measured by ND-CPTs revealed that the lumpy fill layer is highly
heterogeneous, consisting of high density zones, with large voids that are filled with
147
very soft clay that are found at this site. The lowest density measured in the lumpy fill
layer is about 14 kN/m3. The lumpy fill layer after the placement of a sand surcharge
has consolidating and over-consolidated zones. The over-consolidated zone is
consistent with that of the original lump while the consolidating zone is due to the
infilling of inter-lump voids with very soft clay and also breakaway little lumps.
In addition, it is necessary to gain the understanding on the transition from the
initial state of a lumpy fill to the ultimate state of lumpy fill layer so that the large
dredged clay lumps can be used for land reclamation as fill materials. A case study will
be carried out to evaluate the ultimate state of a reclaimed land constructed using large
clay lumps and this will be discussed in next chapter.
148
Figure 5.1 Geological locations of project site and pilot test areas (TA 1, TA 2 and TA 3) in the reclamation site.
Figure 5.2. Typical Geological Profiles for seabed soils prior to reclamation.
-50
-45
-40
-35
-30
-25
-20
-15
-10
-5
0
Dep
th (
mC
D)
Lower Marine Clay
Intermediate ClaySand
Upper Marine Clay
Surface Soft Marine Clay
Weathered granite
Seawater
C182 C183 A39/C184
?
149
Figure 5.3. Typical soil profiles and index properties at the project site.
0
5
10
15
20
25
30
35
40
0 20 40 60 80 100 120
Water Content (%)
Dept
h be
low
Sea
bed
(m)
Wp
Wn
WL
0
5
10
15
20
25
30
35
40
0 20 40 60 80 100
Soil Composition (%)
Dept
h be
low
Sea
bed
(m)
Clay
Silt
0
5
10
15
20
25
30
35
40
0.0 0.4 0.8 1.2 1.6Liquidity Index
Dept
h be
low
Sea
bed
(m)
0
5
10
15
20
25
30
35
40
0.0 0.2 0.4 0.6 0.8 1.0 1.2
Activity
Dept
h be
low
Sea
bed
(m)
Lower Marine Clay
Intermediate Layer
Upper Marine Clay
SSMC
150
(a) (b) (c) (d) Figure 5.4 Geotechnical Characteristics of Seabed Soils prior to reclamation (a) Undrained Shear Strength (b) Sensitivity (c) Remoulding loss (d) Swelling Potential.
0
5
10
15
20
25
30
35
40
0 40 80 120 160 200
Undrained Shear Strength (kPa)
Dept
h be
low
Sea
bed
(m)
UU Test
UC Test
Nkt = 8
Nkt = 10
Nkt = 12
0
5
10
15
20
25
30
35
40
1 2 3 4 5 6 7 8 9 10Sensitivity of Clays, St
Dept
h be
low
Sea
bed
(m)
2 31 4
1 - Low Sensitivity2 - Medium Sensitivity3 - Sensitive4 - Extra-sensitive
0
5
10
15
20
25
30
35
40
0 20 40 60 80 100Remoulding loss (%)
Dept
h be
low
Sea
bed
(m)
0
5
10
15
20
25
30
35
40
0 10 20 30 40Sw elling Potential (%)
Dept
h be
low
Sea
bed
(m)
Very High High
SSMC
Upper Marine Clay
Intermediate Layer
Lower Marine Clay
151
Figure 5.5 Geotechnical Characteristics of Seabed Soils prior to reclamation (a) Preconsolidation pressure (b) OCR (c) Compression index (d) Swelling index
0
5
10
15
20
25
30
35
40
0 100 200 300 400 500 600 700 800
Preconsoildation Pressure (kPa)
Dep
th b
elow
Sea
bed
(m)
σv'
0
5
10
15
20
25
30
35
40
1.0 2.0 3.0 4.0 5.0 6.0 7.0 8.0
OCR
Dep
th b
elow
Sea
bed
(m)
0
5
10
15
20
25
30
35
40
0.0 0.2 0.4 0.6 0.8 1.0 1.2 1.4
Compression Index, Cc
Dep
th b
elow
Sea
bed
(m)
0
5
10
15
20
25
30
35
40
0.0 0.1 0.2 0.3 0.4
Swelling index, Cr
Dep
th b
elow
Sea
bed
(m)Intermediate
Layer
Lower Marine Clay
Upper Marine Clay
SSMC
152
Figure 5.6 Typical dredged materials obtained from (a) Surface soft marine clay
(b) upper marine clay.
(a)
(b)
~ 2 m
153
Figure 5.6 Typical dredged materials obtained from (c) Intermediate layer
(d) Lower marine clay.
(c)
(d)
1m
154
Figure 5.7 Dumping of dredged clay lumps using bottom opening barge.
Figure 5.8 Schematic profile of reclamation with dredged clay lumps and sand Surcharge.
Barge Size Width : ~ 10m Length : ~20m Height : ~ 5m Volume : ~ 900 – 1000m3
Seabed
Sand Fill
~9m
~8m
Dredged Clay Lumps
Inter-lump voids filled with small clay blocks
and water
155
Figure 5.9 Photographic View of the Marine Cone Penetration system used in field investigation
Figure 5.10 Photographic View of the CPT crawler used in field investigation on land.
Marine Cone Penetration System Dimensions of Platform: 60 ft x 26 ftCounter weight = 10 ton
Diameter of Counter weight = 3.4m
Reaction frame or Tower and
Hydraulic Penetration system
Control Unit
156
Details at Location ‘A’
Figure 5.11 Layout of ND-CPT in site investigation at TA 2 (Stage 1 and Stage 2).
Legend
ND-CPT
99m
100m
11m
10m
110B
109C
11m
10m108107
98 10099
106105104103102
91C 92 93 97969594
20
30
60B
8681
71C
82 83 84 85
72 73 74
61 62
52 53
63 64
11
40C
2 3 4 5
12 13 14 15
2524
121C
2321 22
31
41
32
42
33C 34 35
4543 44
54 55
65C
76
66
77
67 68 70
80
69
79
90898887
47
59
49 5048
5857
101B
1B
26B
10B
78B
75B
51B
56
46
36C 37 38 39
2928C27
19C
181716
987
A
10m
11m
119 56
112111B
4645 118
115
55
113
117116
114
120
11m
10m
157
Figure 5.12 Typical cone resistance, pore pressure and wet density profiles at location RI 111B in TA 2 (Stage 1). Figure 5.13 Typical cone resistance, pore pressure and wet density profiles at location RI 104 in TA 2 (Stage 1).
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.2 0.4 0.6 0.8
Pore water pressure, u2 (MPa)
Dept
h(m
CD)
RI 111B
Hydrostatic
Lumpy Fill Layer
Seawater
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.2 0.4 0.6 0.8 1.0 1.2
Corrected cone resistance, qt, (MPa)
Dept
h(m
CD)
RI 111B
Clay Lump
Seabed Soil
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
012 13 14 15 16 17 18 19 20
Wet Density (kN/m3)
Dept
h(m
CD)
RI 111B
Inter-lump voids filled withwith slurry
Clay Lump
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.2 0.4 0.6 0.8 1.0 1.2Corrected cone resistance, qt, (MPa)
Dep
th(m
CD
)
RI 104
Seabed Soil
Seawater
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.2 0.4 0.6 0.8
Pore water pressure, u2 (MPa)
Dep
th(m
CD
)
RI 104
Hydrostatic
Lumpy Fill Layer
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
012 13 14 15 16 17 18 19 20
Wet Density (kN/m 3)
Dep
th(m
CD
)
RI 104
Clay Lump
Inter-lump voids filled w ith slurry
158
Figure 5.14 Typical cone resistance, pore pressure and wet density profiles at location RI 13 in TA 2 (Stage 1).
Figure 5.15 Typical cone resistance, pore pressure and wet density profiles at location RI 101B in TA 2 (Stage 1).
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.2 0.4 0.6 0.8
Pore water pressure, u2 (MPa)
Dept
h (m
CD)
RI 13
Hydrostatic
Clay Lump
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.2 0.4 0.6 0.8 1.0 1.2 1.4
Corrected cone resistance, qt, (MPa)
Dept
h(m
CD)
RI 13
Seawater
Seabed Soil
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
012 13 14 15 16 17 18 19 20
Wet Density (kN/m3)
Dept
h (m
CD)
RI 13
Clay Lump
Inter-lump voids filled with soft clay slurry
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.4 0.8 1.2 1.6 2.0
Corrected cone resistance, qt, (MPa)
Dept
h(m
CD)
RI 101B
Seabed Soil
Seawater
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
0
0.0 0.2 0.4 0.6 0.8Pore water pressure, u2 (MPa)
Dept
h (m
CD)
RI 101BHydrostatic
Lumpy fill layer
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
012 13 14 15 16 17 18 19 20
Wet Density (kN/m3)
Dept
h (m
CD)
RI 101B
Inter-lump voids filled with slurry
Clay Lump
Clay Lump
Clay Lump
159
Figure 5. 16 Typical background count profiles obtained for homogenous soils Clay deposits (b) Sandy deposits (Nobuyama, 2000).
Figure 5.17 Typical RI count and Background count profiles obtained for highly heterogeneous lumpy fill site.
0
5
10
15
20
25
30
0 50 100 150 200 250 300 350 400Background count (CPS)
Dept
h (m
)
Drammen Clay (Norw ay)Kinkai BayHachirogata (Akita)
(a)
0
5
10
15
20
25
30
0 50 100 150 200 250 300 350 400Background count (CPS)
Dept
h (m
)
Holmen Sand (Norw ay)Vancouver Sand (Canada)Kamigaw a Sand (Chiba)Higashi Ohgishima Sand (Kanagaw a)
(b)
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
0600 700 800 900 1000 1100 1200
RI count (CPS)
Dept
h(m
CD)
RI 115 RI 116
RI 118 RI 120
RI 45 RI 111
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
050 100 150 200 250 300
Background count (CPS)
Dept
h(m
CD)
RI 115 RI 116RI 118 RI 120RI 45 RI 111Average BG
(a)
(b)
160
Figure 5.18 Comparison of estimated wet density using actual measured background count and average background count.
Figure 5.19 Diagram of Single Probe Nuclear-Density Cone Penetrometer (ND-CPT)
(All dimensions in millimeters).
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
012 13 14 15 16 17 18 19 20
Wet Density (kN/m3)
Dept
h(m
CD)
RI 45Average BG
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
012 13 14 15 16 17 18 19 20
Wet Density (kN/m3)
Dept
h(m
CD)
RI 115Average BG
Detector-1 Detector-2 Gamma source
1538.83
48.6 35.6
161
Figure 5.20. Comparison of wet density profiles measured by double and single probe ND-CPTs.
0
2
4
6
8
10
12
14
16
18
20
22
12 14 16 18 20 22Wet Density (kN/m3)
Dept
h(m
)
RI 91-Single Probe(07/01/2004)RI 91-Double Probe(09/12/2003)
Sand Fill
Lumpy Fill
0
2
4
6
8
10
12
14
16
18
20
22
12 14 16 18 20 22Wet Density (kN/m3)
Dept
h(m
)
RI 121-Single Probe(15.01.2004)RI 121-Double Probe(12.12.2003)
Sand Fill
Lumpy FIll
Seabed
0
2
4
6
8
10
12
14
16
18
20
22
12 14 16 18 20 22Wet Density (kN/m3)
Dept
h(m
)
RI 71-Single Probe(09/01/2004)RI 71-Double Probe(09/12/2003)
Sand Fill
Lumpy FIll
0
2
4
6
8
10
12
14
16
18
20
22
12 14 16 18 20 22Wet Density (kN/m3)
Dept
h(m
)
RI 28-Single(09/01/2004)RI 28-Double(10/12/2003)
Sand Fill
Lumpy Fill
Seabed
162
Figure 5.21 Typical Cone resistance, Pore pressure and wet density profiles obtained at location RI 91
Figure 5.22 Typical Cone resistance, Pore pressure and wet density profiles obtained at location RI 71.
-18
-16
-14
-12
-10
-8
-6
-4
-2
0
2
40 2 4 6 8 10 12 14 16
Corrected cone resistance, qt, (MPa)
Dept
h(m
CD)
RI 91 (Stage 2)(09/12/2003)
RI 91 (Stage 1)(30/08/2002)
Lumpy Fill Layer
-18
-16
-14
-12
-10
-8
-6
-4
-2
0
2
40.0 0.2 0.4 0.6 0.8
Pore water pressure, u2 (MPa)
Dept
h(m
CD)
RI 91 (Stage 2) (09/12/2003)Hydrostatic RI 91 (Stage 1) (30/08/2002)
Sand FIll
-18
-16
-14
-12
-10
-8
-6
-4
-2
0
2
410 12 14 16 18 20 22
Wet Density (kN/m 3)
Dept
h(m
CD)
RI 91 (Stage 2)(09/12/2003)RI 91 (Stage 1)(30/08/2002)
Seabed
-18
-16
-14
-12
-10
-8
-6
-4
-2
0
2
40.0 2.0 4.0 6.0 8.0 10.0
Corrected cone resistance, qt, (MPa)
Dept
h(m
CD)
RI 71 (Stage 2)(09/12/2003)
RI 71 (Stage 1)(28/08/2002)
-18
-16
-14
-12
-10
-8
-6
-4
-2
0
2
40.0 0.2 0.4 0.6 0.8
Pore water pressure, u2 (MPa)
Dept
h(m
CD)
RI 71 (Stage 2) (09/12/2003)
Hydrostatic
RI 71 (Stage 1) (28/08/2002)
Lumpy Fill Layer
Sand Fill
-18
-16
-14
-12
-10
-8
-6
-4
-2
0
2
410 12 14 16 18 20 22
Wet Density (kN/m 3)
Dept
h(m
CD)
RI 71 (Stage 2)(09/12/2003)RI 71 (Stage 1)(28/08/2002)
Seabed
163
1
10
100
1000
-0.6 -0.4 -0.2 0 0.2 0.4 0.6 0.8 1 1.2 1.4
Pore Pressure Ratio Bq
Nor
mal
ized
Con
e R
esis
tanc
e Q
t
SeabedLumpy FillSand Fill
1 2
3
Increasing sensitivity
4
IncreasingOCR 5
6
7
RI- 91 (Stage 2)
1
10
100
1000
-0.6 -0.4 -0.2 0 0.2 0.4 0.6 0.8 1 1.2 1.4
Pore Pressure Ratio Bq
Nor
mal
ized
Con
e R
esis
tanc
e Q
t
SeabedLumpy FillSand Fill
12
3
Increasing sensitivity
4
IncreasingOCR 5
6
7
RI-71 (Stage 2)
Zone Soil Zone Soil
1 Sensitive, Fine Grained 5 Sand mixtures; silty sand to sand silty
2 Organic soils-peats 6 Sands; clean sands to silty sands
3 Clays-clay to silty clay 7 Gravelly Sand to sand
4 Silt mixtures clayey silt to silty clay
Figure 5.23 Robertson (1990) charts for ND-CPT data at locations RI 91 and RI 71.
(a)
(b)
164
Figure 5.24 Variation of wet density profiles within lumpy fill layer (a) at location RI 91 (b) at location RI 71 (c) at location RI 36.
-14
-13
-12
-11
-10
-9
-8
-7
-6
-510 12 14 16 18 20 22
Wet Density (kN/m 3)
Dept
h(m
CD)
RI 71 (Stage 2)(09/12/2003)RI 71 (Stage 1)(28/08/2002)
(b)
Softening of edges of the clay lumps
-14
-13
-12
-11
-10
-9
-8
-7
-6
-510 12 14 16 18 20 22
Wet Density (kN/m3)
Dept
h(m
CD)
RI 91 (Stage 2)(09/12/2003)
RI 91 (Stage 1)(30/08/2002)
Inter-lump voids filled w ith slurry
Clay lump
Clay lump
Clay Lump
Inter-lump voids filled with slurry
(a)
-14
-13
-12
-11
-10
-9
-8
-7
-6
-510 12 14 16 18 20 22
Wet Density (kN/m3)
Dept
h(m
CD)
RI 36 (Stage 2)(12/12/2003)
RI 36 (Stage 1)(03/09/2002)
(c)
165
Figure 5.25 Typical cone resistance, pore pressure and wet density profiles obtained
from ND-CPT for seabed clays.
Figure 5.26 Typical e-logσv′ curves obtained from ND-CPT results for seabed soils.
-28
-26
-24
-22
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.5 1.0 1.5 2.0 2.5
Corrected cone resistance, qt, (MPa)
Dept
h(m
CD)
RI 04
Surface Soft Marine clay
Lower marine clay
-28
-26
-24
-22
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
00.0 0.2 0.4 0.6 0.8 1.0
Pore water pressure, u2 (MPa)
Dept
h(m
CD)
RI 04Hydrostatic
Seawater
-28
-26
-24
-22
-20
-18
-16
-14
-12
-10
-8
-6
-4
-2
012 14 16 18 20 22
Wet Density (kN/m 3)
Dept
h(m
CD)
RI 04
Intermediate layer
0.0
0.5
1.0
1.5
2.0
2.5
3.0
3.5
4.0
1 10 100 1000
Effective vertical Pressure, σv' (kPa)
Voi
d ra
tio, (
e)
RI 04RI 02
166
Figure 5.27 One-dimensional compression and swelling curves for reconstituted soil samples obtained from the Singapore marine clay at Pulau Tekong Island.
Figure 5.28 One-dimensional compression and swelling curves for reconstituted soil
samples in terms of void index.
0.0
0.5
1.0
1.5
2.0
2.5
3.0
1 10 100 1000 10000
Effective vertical pressure, σv' (kPa)
Void
ratio
, (e)
ICL
-4.0
-3.0
-2.0
-1.0
0.0
1.0
2.0
3.0
4.0
1 10 100 1000 10000
Effective vertical pressure, σv' (kPa)
Void
Inde
x, (I
v)
ICL
ICL Proposed by Burland (1990)
167
Figure 5.29 Comparison of intact compression curves obtained from ND-CPT results with Intrinsic Compression Line (ICL) and Sedimentation Compression Line (SCL) for seabed clays.
-4.0
-3.0
-2.0
-1.0
0.0
1.0
2.0
3.0
4.0
1 10 100 1000
Effective vertical Pressure, σv' (kPa)
Voi
d in
dex,
(Iv)
RI 04
ICL
SCL
OC
NC
(a)
-4.0
-3.0
-2.0
-1.0
0.0
1.0
2.0
3.0
4.0
1 10 100 1000
Effective vertical Pressure, σv' (kPa)
Void
inde
x,(I
v)
RI 02
ICL
SCL
OC
NC
168
-4.0
-3.0
-2.0
-1.0
0.0
1.0
2.0
3.0
4.0
1 10 100 1000Effective vertical pressure, σv' (kPa)
Void
Inde
x, (I
v)
RI 36-Stage 1 (03/09/2002)
RI 36-Stage 2 (12/12/2003)
SCL
ICL
-4.0
-3.0
-2.0
-1.0
0.0
1.0
2.0
3.0
4.0
1 10 100 1000Effective vertical pressure, σv' (kPa)
Voi
d In
dex,
(Iv)
RI 91-Stage 1 (30/08/2002)
RI 91-Stage 2 (09/12/2003)
SCL
ICL
Figure 5.30 Comparison of intact compression curves obtained from ND-CPT results with ICL and SCL for lumpy fill layer.
169
Figure 5.31 Comparison of intact compression curves obtained from ND-CPT results with ICL and SCL for lumpy fill layer.
-4.0
-3.0
-2.0
-1.0
0.0
1.0
2.0
3.0
4.0
1 10 100 1000Effective vertical pressure, σv' (kPa)
Void
Inde
x, (I
v)
RI 109-Stage 1 (12/08/2002)
RI 109-Stage 2 (09/12/2003)
SCL
ICL
-4.0
-3.0
-2.0
-1.0
0.0
1.0
2.0
3.0
4.0
1 10 100 1000Effective vertical pressure, σv' (kPa)
Voi
d In
dex,
(Iv)
RI 71-Stage 1 (28/08/2002)
RI 71-Stage 2 (09/12/2003)
SCL
ICL
170
Figure 5.32 Typical void index versus depth profiles used for identifying the compact and less compact zones within the lumpy fill layer.
-14
-13
-12
-11
-10
-9
-8
-7
-6-4 -3 -2 -1 0 1 2 3 4
Void IndexD
epth
(mC
D)
RI 91 (Stage 2)(09/12/2003)RI 91 (Stage 1)(30/08/2002)
Less Compact
Compact
-14
-13
-12
-11
-10
-9
-8
-7
-6-6 -5 -4 -3 -2 -1 0 1 2 3 4 5 6
Void Index
Dep
th(m
CD
)
RI 71 (Stage 2)(09/12/2003)
RI 71 (Stage 1)(28/08/2002)
Less Compact
Compact
-14
-13
-12
-11
-10
-9
-8
-7
-6-4.0 -3.0 -2.0 -1.0 0.0 1.0 2.0 3.0 4.0
Void Index
Dep
th(m
CD
)
RI 36 (Stage 2)(12/12/2003)
RI 36 (Stage 1)(03/09/2002)
Compact
Less Compact
171
Figure 5.33 Variation of estimated remoulded undrained shear strength profiles within lumpy fill layer.
-14
-13
-12
-11
-10
-9
-8
-7
-6
-50 40 80 120 160 200
Remoulded shear strength, Sur (kPa)
Dept
h(m
CD)
RI 91 (Stage 2)(09/12/2003)
RI 91 (Stage 1)(30/08/2002)0.25∗σ v '
-14
-13
-12
-11
-10
-9
-8
-7
-6
-50 40 80 120 160 200
Remoulded Shear strength, Sur (kPa)
Dept
h(m
CD)
RI 40 (Stage 2)(10/12/2003)
RI 40 (Stage 1)(09/09/2002)
0.25∗ σ v '
-14
-13
-12
-11
-10
-9
-8
-7
-6
-50 40 80 120 160 200
Remoulded shear strength, Sur (kPa)
Dept
h(m
CD)
RI 33 (Stage 2)(12/12/2003)
RI 33 (Stage 1)(07/08/2002)
0.25∗ σ v '
-14
-13
-12
-11
-10
-9
-8
-7
-6
-50 40 80 120 160 200
Remoulded shear strength Sur (kPa)
Dept
h(m
CD)
RI 71 (Stage 2)(09/12/2003)
RI 71 (Stage 1)(28/08/2002)
0.25∗σv'
172
Figure 5.34. Photographic view of Singapore marine clay lump of 205 mm diameter before and after three-dimensional swelling.
Figure 5.35. Variation of water content at end of three-dimensional swelling clay lumps of diameter, D= 205mm (after Robinson et al. 2004).
0
2
4
6
8
10
12
14
16
18
20
42 44 46 48 50 52 54Water content (%)
Dep
th (c
m)
D/2 D/4 D/4
173
0 0.4 0.8 1.2 1.6 2 2.4 2.8 3.2 3.6 4 4.4 4.8 5.2 5.6In-situ void ratio
0
100
200
300
400
500
600
700
800
Freq
uenc
y
Stage 1 (-3mCD)-TA 2
Average void ratio = 2.18
No of data's = 11643
Stage 2 (+4mCD)-TA2
Average void ratio = 2.09
No of data's = 11181Stage 1Stage 2Normal Fit- Stage 1Normal Fit- Stage 2
Figure 5.36 Histogram of frequency of in-situ void ratio measured by the ND-CPT for
the lumpy fill layer in Stage 1 and Stage 2.