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describe geotechnical aspect of the landfill barrier and liner system. strength of liner, geosynthetics, etc
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Mechanical behaviour of landfill barriersystemsL. Edelmann, PhD, DGGT, M. Hertweck, PhD, SIA, USIC and P. Amann, PhD,COST, DGGT, DIA, SIA
& Land®lls may need to be surrounded by
engineered liner systems to prevent dan-
gerous leakage to the environment.
Depending on the location of the liner, that
is, at the bottom, surface or sides of the
land®ll, the system may be highly stressed
in bending or shear. Full-scale tests and
additional ®eld measurements were
carried out to de®ne the ultimate state of
the permeability of horizontal and vertical
compacted clay liners. The results of these
tests can be used in the overall design of
such land®ll liners. The testing equipment
developed may be used to improve new
system designs or to test alternative com-
binations of materials.
Keywords: geotechnical engineering; land-
®ll; research & development
Notationcc cohesion
h height
K hydraulic conductivity
Ko initial hydraulic conductivity
k lateral stress ratio
R radius of curvature
g unit weight
ee strain
een volumetric strain
eeg shear strain
y volumetric water content
f internal friction angle
IntroductionTo protect the environment against leakage
from land®lls, multi-barrier systems have been
developed. One component of such systems
involves technical barriers, which surround the
deposits. Within a land®ll, it is possible to
distinguish between bottom, surface and side
liners.
2. As a ®rst requirement, the arti®cial
barrier must be technically impermeable, which
means low conductivity (e.g. k � 1079 m/s)
and stressed by a `low' hydraulic gradient
(®eld: i � 2; but often in laboratory tests,
i � 30).
3. The sealing component of most liner
systems consists of, or is combined with, clayey
materials. The conductivity will increase and
the containment capacity will be lost due to
deformation or cracking. Bending occurs with
non-uniform settlements of the subsoil (bottom
liner) or of the waste material (capping) (Fig. 1).
The latter will also be in¯uenced by the
sequence of ®lling. Steep wall liners are mainly
strained by shear deformation due to `silo'
conditions, with di�erential settlements
between the deposited material and the side
walls. Additionally, kinematic failure mechan-
isms need to be analysed (Fig. 2).
4. Sloped liners are strained under com-
bined conditions. While the tendency for
bulging is predominant, it may occur in
conjunction with shear failure. The sealing
system can become unserviceable because of
large lateral deformations or collapse under
shear failure. Large lateral displacements can
cause increasing volumetric strain and there-
fore an increase in hydraulic conductivity.
Considering the inclined drainage layer as a
solid body, overturning around the toe of the
wall is also possible. Gravity and external
loads decrease safety with respect to bearing
capacity failure.
5. Few laboratory or ®eld investigations of
the stress±strain behaviour of barrier systems
exist. In this paper, the authors report results of
1:1 scale tests performed with horizontal and
vertical barrier systems in combination with
®eld measurements, and give suggestions for
practical applications. The idea for these inves-
tigations came from two land®lls in Germany
where the last author was called in for expert
consultations. The experimental investigations
were performed at the Technical Universities at
Darmstadt (horizontal barrier) and Zurich (ver-
tical barrier).
Horizontal barrier system
Principle of investigations
6. The experimental investigations con-
centrated on the bending e�ects of a thin
(0´6 m) mineral liner.1 First, the damage
criterion had to be de®ned. It was decided to
use an increase in water content in the
drainage layer underneath the mineral liner
(Fig. 3) as a sign of the beginning of leakage.
With this increase in water content it was
possible to detect leakage due to cracking.
Therefore, the liner was covered with a 0´6 m
layer of water during the test. After some
initial tests, it was found that the best way to
induce bending was by lowering the founda-
Lorenz Edelmann,
Consulting Engineer,
Amann Infutec
Consult Ltd, Muhltal
Michael Hertweck,
Consulting Engineer,
SKS Engineers Ltd,
Zurich
Peter Amann,
Professor of Soil
Mechanics and
Foundation
Engineering,
Institute of
Geotechnical
Engineering, Swiss
Federal Institute of
Technology, Zurich
215
Proc. Instn
Civ. Engrs
Geotech. Engng,
1999, 137, Oct.,
215±224
Paper 11855
Written discussion
closes 31 March 2000
Manuscript received
26 October 1998;
revised manuscript
accepted 27 May
1999
tion bed of the liner to simulate conditions for
local settlement.
Testing equipment
7. The simulator is shown in Figs 3 and 4. The
support construction consists of two parts: the
peripheral support and the central support with
a lowering capacity. The central support was
made of 19 cylindrical rubber cushions, con-
centrically arranged and ®lled with water. The
arrangement of the rubber cushions formed three
independently operated ring circles with cushion
No. 1 as the ®rst circle in the middle (Fig. 3).
8. The support construction could be
lowered by the hydraulically operated cushions
in a highly controlled way to simulate sub-
sidence and deformation. By removing di�erent
quantities of water from the rings of cushions, a
vertical displacement and a bending deforma-
tion of the barrier model could be imposed.
9. The 0´6 m thick barrier was constructed
by compacting approximately 16 t of soil
material placed on the top of the support
elements and the 0´25 m thick drainage layer
made of sand. The leakage was measured by
time domain re¯ectometry (TDR) probes and
tensiometers in the drainage layer immediately
beneath the barrier. TDR is a method in which
volumetric water content is determined from
dielectric properties of wet soil.2 Thirty TDR
probes and four tensiometer measuring lines
were installed in a grid which enabled the
measurement of changes in water content and
the precise localization of percolation and
leakage spots. The deformation subsidence was
measured by displacement transducers both on
top and at the bottom of the barrier. A
subsidence velocity of Dh=4 mm per day in
the centre of the barrier was selected.
Material
10. Two natural soil types judged to be
characteristic of the range of materials used in
soil liner construction were selected for the
tests, namely silt and clay (Table 1). The silt
had a relatively low plasticity. The material
was susceptible to imposed deformations and,
even though it represented the lower limit of
the quality range of materials, is frequently
used in land®ll construction. The clay exhibited
higher plasticity and more or less represented
the upper limit of liner materials quality used
in construction.
Test results and analysis
11. Three large-scale tests were carried out,
two with silt and one with clay, lasting up to
three months each. With the tests using the silt,
the ®rst leakage was measured at a maximum
settlement of 3´15 cm in the bottom centre (Fig. 5).
Initial stateDeformed state
Soil liner
R
Fig. 1. Deformation of horizontal barriers
2
1
(a) (b) (c) (d)
Fig. 2. Failure mechanism of steep-slope barrier systems: (a) bulging;
(b) shear failure; (c) overturning; and (d) bearing capacity failure.
Fig. 3. Cross-section of testing equipment (horizontal barrier)
216
EDELMANN ET AL.
Additional leaks were observed in the range of
maximum subsidence of 3´15±5´53 cm. The
deformation of the barrier corresponded to an
arc of a circle. The radius of curvature for the
maximum subsidence in the centre at the onset
of leakage can be calculated as the limiting
value for acceptable deformation. For a sub-
sidence of 3´15 cm the radius of curvature was
calculated to be R=70 m for the silt (Fig. 5).
The radius of curvature corresponding to a
subsidence of 5´53 cm was calculated to be
R=40 m. During dismantling of the models, no
cracks were observed visually.
12. In the deformation test with clay, the
testing apparatus support was lowered to its
maximum extent of h=38 cm without any
failure occurring. The corresponding radius of
curvature was calculated to be R=6 m. The
clay barrier was still intact at that subsidence
condition. Permeability tests (i=30) were
carried out on extracted undisturbed samples
of the deformed clay barrier, yielding an
average coe�cient of permeability of
k=2´86 10710m/s. A comparison with the
results of permeability measurements made
prior to the test (Table 2) indicates that no
signi®cant change in permeability occurred for
the clay in spite of a calculated average volume
expansion of the samples in the deformation
test of eev =+5´6%.
13. A ®nite element analysis was carried
out to investigate the deformed barrier
numerically. The stress±strain behaviour was
modelled using an elastic Mohr±Coulomb
plastic relationship. Therefore, the attention
was focused on the strain distribution in the
barrier. For the silt, the maximum horizontal
strain at the outer edge area of the barrier,
where the ®rst leaks were identi®ed, was
calculated to be eeh =+0´2% (Fig. 6). For the
clay, the maximum horizontal strain at the
outer edge area of the barrier was about
eeh =+1´3%.
Results of in situ measurements
14. As a part of an industrial and municipal
land®ll, a 30 m thick waste body of sludge from
industrial waste water treatment was deposited
in Hessia, Germany, and covered by municipal
waste (Fig. 7). The two di�erent waste bodies
are separated by a thin intermediate liner
system composed of a 0´75 m thick clay
composite liner. The material properties of the
sludge have been reported by Amann et al.3 The
liner system was subject to imposed deforma-
tions due to the consolidation settlements of the
sludge itself, its strongly pronounced creep
behaviour and also from settlements caused by
the weight of the municipal waste (Fig. 7).
15. A measuring programme was developed
for in situ investigations of the deformation
behaviour of the intermediate liner system and
the industrial sludge.4 As a part of the complete
Table 1. Geotechnical parameters of tested materials
Soil parameters Units Horizontal tests Vertical tests
Silt Clay Barrier Weak
suppport
Sti�
supportField Test
Classi®cation Ð Ð Ð CL CL Peat GP
Grading C, S, S, G Ð % 18/71/11/0 48/44/8/0 17/60/23/0 23/36/23/19 Ð 0/10/22/58
Permeability K m/s 66 10710 2´96 10710 0´56 10711 56 10711 Ð Ð
Water content w % 17´7 17´5 19´8 21 180 3
Liquid limit wL % 31´4 42´8 39´5 47 Ð Ð
Plastic limit WP % 20´1 20´6 15´2 26 Ð Ð
Plasticity index IP % 11´3 22´2 24´3 22 Ð Ð
Shrinkage limit wS % 16´5 17´2 15´3 16´6 Ð Ð
Proctor density rpr t/m3 1´81 1´78 Ð 17´2 0´5 21´7
Opt. water content w % 15´2 16´7 Ð 21 90 6´3
Uniax. compr. qqu kN/m2 230 294 Ð Ð Ð Ð
Cohesion cc ' kN/m2 23 20 20 22 Ð Ð
Friction angle f' Degrees 27 27 18 24 30 >35
CC-modulus ME MN/m2 Ð Ð 5´2±12 6´5±23 1´4±7´7 28±58
Fig. 4. Testing
equipment for
horizontal barrier
systems (D= 4´2 m)
217
MECHANICAL BEHAVIOUR
OF LANDFILL BARRIER
SYSTEMS
programme, an approximately 170 m long
¯exible tube placed in the upper drainage layer
was installed for hydrostatic pro®le gauge
measurements to investigate the settlements
of the intermediate liner along the tube. The
results of the hydrostatic pro®le gauge meas-
urements show comparatively continuous
settlement curves (Fig. 8).
16. The measurements were carried out in
1 m long sections. The radii of curvature were
back-calculated from the data after carrying out
a regression analysis to smooth out the settle-
ment curves. Thus, the minimum radius of
curvature back-calculated with the measure-
ments from August 1996 were found to be in
the order of R=20±30 m. In comparison with
the large-scale test results with clay, it is
concluded that the current deformation state
was within the serviceability limit of the
intermediate liner system. This is in accordance
with the ®eld leakage measurements.
Vertical barrier system
Principle of investigation
17. Vertical or steep-sloped barriers are
used in pits, for example deep quarries. The
mineral component of the sealing must be
constructed simultaneously with the ®lling of
the waste, which acts as a retaining material.
The most stressed component of these barrier
systems is the footing, especially the connection
between the vertical and the horizontal parts. It
was decided to concentrate the research on this
area by 1:1 scale loading tests.5 Higher con-
struction stages up to a height of 35 m were
simulated. The various weights of the compo-
site construction were simulated by stepwise
and di�erent additional loading with loading
beams (see Fig. 9). The investigations included
50
45
40
35
30
25
20
15
10
0
5
7 14 21 28 35 42 492
4
6
8
10
12
14
16
18
20
22100 90 80 70 60 50 40 30 20 10 0
Radius of curve, R: m
Testing time, t: days
Displacement against testing tube
Wat
er c
onte
nt, θ
: vol
-%
Dis
plac
emen
t, h:
cm
TDR12 TDR13TDR25 TDR24 TDR3
Fig. 5. Water content measurements of the ®rst leakage (silt)
Table 2. Summary of strains and permeability of horizontal and vertical barriers
Horizontal barrier: Notation Units Model tests Laboratory tests Field
measurements
Silt Clay Silt Clay Clay
eeh % 0´2 >1´3 Ð Ð Ð
R m 70 6 Ð Ð 20±30
eev % Ð Ð Ð +5´6 Ð
[K0] m/s Ð Ð [66 10710] [2´96 10710] Ð
K m/s Ð Ð Ð 2´86 10710 Ð
Vertical barrier:
Waste (support):
Notation Units Silt Silt Silt
Weak Sti� Weak Sti� Weak
eeh % 8 1 Ð Ð 5±9
eez % 710 76 Ð Ð 74
eev % 76 76 Ð Ð 75
eeg % 10±16 eev* eeg Ð Ð 17
[K0] m/s Ð Ð 76 10711 3610711 Ð
K m/s Ð Ð 26 10711 16 10711 Ð
Fig. 6. Isograph of horizontal strains (silt, R= 70 m)
218
EDELMANN ET AL.
varying the relative sti�nesses of the barrier
and the waste material.
Testing equipment
18. The installed model and the deforma-
tion measuring device are shown in Figs 9 and
10. A typical wall sealing system with a width
of 1´1 m made of a silty clay was reproduced.
A ®nal height of the composite construction of
37 m was simulated by the application of
surcharge loads. The inclined natural wall
(e.g. rock wall) was evened with a bituminous
layer. Two tests with the same sealing material
but with di�erent waste material were carried
out. The ®rst test used a weak material,
modelling MSW (municipal solid waste); the
second used a sti� material, modelling MSW
slag.
19. The load was increased on the sealing
system and on the waste deposit alternately.
Generally, the wall sealing system was loaded
®rst, to simulate preconstruction in the ®eld.
Up to a height of 12 m, 1 m loading increments
were used with 3 m increments above 12 m.
Both tests were executed with the same loading
stages. Each test required one year.
20. The deformations, stresses, pore water
pressures and the volumetric water content in
the liner were measured during loading. Prior-
ity was given to the deformation measurements
in the sealing, which were measured by dis-
placement transducers (LVDTs). The arrange-
ment of the transducers gave a framework of
eight rectangular grid elements (Fig. 10). The
volumetric strain could be calculated in each
one. The stress state could also be recorded at
di�erent levels using pressure cells (GloÈ tzl
type). The volumetric water content was
observed by measuring the electrical resistance.
In the waste, no measurements were made. A
detailed description of the measuring device is
found in reference 5.
Material
21. The parameters of the material used are
listed in Table 1. For the weak support a peat±
compost mixture was used, having similar
deformation characteristics to MSW.5
Test results and analysis
22. In both full-scale tests the proposed
height of 37 m was reached without any failure
or loss of serviceability of the wall sealing
system. After the ®rst test (using weak waste
material), the wall sealing system showed a
total surface settlement of 10% of the actual
model height (4´0 m). The deformation of the
body of waste near the gabions was 28% of the
actual height of the waste material. Up to a
simulated height of 17 m, the waste material
slid along the gabions, producing an average
shear stress of 30 kN/m2 over the height of the
model, after which the waste material adhered
to the gabions. The average shear stress then
increased with height up to a maximum of
90 kN/m2.
23. The deformations in the second test
were smaller; at the top of the wall sealing a
total settlement of 6% of the actual model
height was measured. The settlement of
the body of waste was of the same order
of magnitude as the liner. The mobilized
shear stress along the gabions was constant
(20 kN/m2). In the ®rst full-scale test, a large
lateral strain of the sealing of ee h = 8% was
measured at the maximum simulated height. In
360
350
340
330
320
310
300
Leve
l: m
+N
M
240 220 200 180 160 140 120 100 80Horizontal tube length: m
Municipal waste
Intermediate liner
Industrial sludge
Subsoil
12/95
10/9612/95
11/93
4/96
7/94
3/92 3/92
Fig. 7. Cross-section
of Asslar land®ll
336
334
332
330
328
326
324
322
320
Leve
l: m
+N
M
160 140 120 100 80 60 40 20 0Length: m
–0·6
–0·4
–0·2
0·2
0·4
0·6
0·8
1·0
1·2
1·4
1·6
0
Set
tlem
ent,
s: m
Zero measurement 11/93Height 6/95Height 8/96
Settlements11/93–6/9511/93–8/96
Fig. 8. Results of
hydrostatic settlement
measurements (Asslar
land®ll)
Fig. 9. Testing
equipment for vertical
barrier systems (6´0 m
long6 5´2 m
wide6 5´0 m high).
On top can be seen the
loading beams
219
MECHANICAL BEHAVIOUR
OF LANDFILL BARRIER
SYSTEMS
the second full-scale test, a horizontal strain of
only ee h = 1% was measured in the sealing. The
horizontal strain of the gabions was measured
to be ee h = 19% in the ®rst test and approxi-
mately zero in the second test. The large
deformation during the ®rst test was required
to mobilize su�cient support in the weak waste
body to prevent failure.
24. The sealing and the gabions acted like a
composite, interlocked construction. The settle-
ment of the wall sealing was not a�ected by the
interface between the wall sealing and the
gabions. No relative movements took place at
this interface and deformations in the wall
sealing and the gabions were of the same order
of magnitude. Unhindered vertical deformation
could take place, resulting in a volume
decrease. The volumetric strain of the ®rst test
is shown in Fig. 11(a). An overall volume
decrease was registered. In both tests, identical
volumetric strains of eev =76% were measured
in the wall sealing but with di�erent distortions
eeg. In the ®rst test (Fig. 11(a)), the grid elements
of the wall sealing (Nos. 4±6) were in e�ect
under triaxial compression with a signi®cant
distortion of eeg=10±16%.
25. The observed plastic deformation of the
upper element (No. 6) during the ®rst test was
accompanied by high excess pore pressures. A
small volume increase occurred at large dis-
tortions but the wall sealing did not fail due
to the bearing capacity reserve. At higher
stress levels, the volumetric deformation came
close to con®ned compression behaviour. In
the second test, the wall sealing was under
con®ned compression during the whole test
(Fig. 11(b)). The observed behaviour during the
®rst test can also be seen in central cores in
earth dams.7 In both tests, the measured stress
ratio k= sH/sV in the wall sealing corre-
sponded to the active state of plastic equili-
brium (Fig. 12(a)). Therefore, the mobilized
coe�cient of earth pressure for the waste body
can be expressed by the active stress ratio of
the sealing, the relationship between the di�er-
ent unit weights and heights assuming that the
strength of the waste is not fully mobilized.
kd � gb
gdhb
hdkb �with hb > hd; hd > 0� �1�
kd � gb
gdkb �with hb � hd� �2�
Fig. 10. Cross-section of testing equipment
(vertical barrier) (dimensions in metres)
20
15
10
5
0
Dis
tort
ion
ε y =
εho
r + ε
ver:
%
20
15
10
5
0
Dis
tort
ion
ε y =
εho
r + ε
ver:
%
0 –2 –4 –6 –8 –10Volumetric strain εv: %
Isotropic compression
Isotropic compression
Triaxial compression
Triaxial compression
Confinedcompression
εv = εy
Confinedcompression
εv = εy
(b)
(a)
el. 4
el. 4
el. 1–3 andel. 7–8
el. 6
el. 5
Constant load atmaximumheight (62 days)
el. 1–3 andel. 7–8
Fig. 11. Volumetric strains plotted against
distortions during the tests with: (a) weak
support; and (b) sti� support
220
EDELMANN ET AL.
where `d' is the deposit and `b' is the barrier.
26. Equation (1) is valid for a parallel
construction and ®lling sequence, and equation
(2) where the steep slope sealing system is
constructed prior to ®lling.
27. A higher stress ratio was obtained
when the liner was constructed prior to ®lling
(Fig. 12(a)). In the earlier construction stages,
higher deformations occurred, but for higher
walls this e�ect became less pronounced.
28. The stress ratios required to prevent
failure were calculated for the proposed failure
mechanisms. The results where construction
takes place before the placement of a 3 m depth
of waste are presented in Fig. 12(b). Further
results are presented in Reference 6. For
inclinations of 708 and greater, bulging of the
wall is also a critical failure mechanism. For
the analysed parameters, the safety reserve for
shear failure will be su�cient. Independent of
wall inclination, the shear failure mechanism
with plastic ¯ow at the toe of the wall (Fig. 2(b),
No. 1) will be more critical than a failure
mechanism across the wall liner (Fig. 2(b),
No. 2).
29. For bearing capacity failure, the width
of the sealing system (wall liner and gabions) is
important with regard to the ®nal height. The
®nal height in the large-scale test for a factor of
safety of 2´0 was 30 m. The height for the MSW
deposit presented, with a width of 3 m, was
56 m. The factor of safety for bearing capacity
failure strongly depends on the inclination of
the wall and the thickness. The ultimate height
decreases signi®cantly for less inclined walls
and thinner liners.
Results of in situ measurements
30. The in situ measurements were carried
out in the wall sealing of a waste deposit for
MSW (Wirmsthal, Germany). The inclination of
the rock wall was 808, evened by concrete
plates covered with a bituminous layer. The
mineral liner consisted of a silty clay (CL)
(Table 1). The thickness of the retaining
gabions which were used to collect leachate was
1 m. They were ®lled with coarse crushed rock.
The wall sealing system was built to a height of
between 3 and 5 m before placement of any
waste. At the time of evaluation the wall
sealing was installed to a maximum height of
20 m, with the total depth of the quarry being
60 m. Two measuring cross-sections were
installed to analyse the deformations and the
stress state of the wall sealing during construc-
tion and after construction (Fig. 13).
31. The lateral extension of the wall
sealing could be obtained from the inclinometer
measurements and is shown in Fig. 14(a). In
cross-section I, the wall sealing widened from a
height of 15 m upwards, causing an overturning
of the gabions towards the waste body as a mode
of movement. In contrast, in cross-section II,
1·2
1·0
0·8
0·6
0·4
0·2
0S
tres
s ra
tio k
= σ
h/σ
v
1·2
1·0
0·8
0·6
0·4
0·2
0
Str
ess
ratio
k =
σh/σ
v
0 20 40 60 80Height of the wall liner: m
(b)
(a)
k d = (γ b/γ d)(h b/h d)k b
(with h b > h d; h d > 0)γ b = 20 kN/m3
γ d = 11 kN/m3
k d = (γ b/γ d)k b (with h b = h d)
k b (calculated φ = 20˚; c′ = 20 kPa)
k b (measured from first large-scale test)
h d = h b – 3 m
σhd
= σhb
d = depositb = barrier
Existing stress ratio
Shear failure (1)
Shear failure (2)
Bulging (overturning)
Bulging (buckling)
Inclination 80˚
Fig. 12. Existing and required stress ratios in the waste body:
(a) comparison of measured and calculated results; and (b) requirements
for di�erent failure mechanism
2·0 m 1·0 m
1·0 m
2·0 m
1·0 m
0·5 m
3·5 m
Leachate collection systemgabions; mesh wire filled withcoarse crushed rock
Rock wall
Sliding layer(bituminous)Ground waterdrainage
Wall sealing
Inclinometersliding micrometer
Earth pressurecells (Glötzl type)
Drainage layer
Displacementtransducer (LVDT)
Fig. 13. Barrier system and measuring device, Wirmsthal land®ll
221
MECHANICAL BEHAVIOUR
OF LANDFILL BARRIER
SYSTEMS
the maximum lateral extension was recorded at
a height of 12 m. This led to a bulging of the
gabions. It can be seen from the in situ
measurements that during the construction of
the sealing system large horizontal strain
occurred in the wall sealing (eeh = 17% at
maximum). The horizontal strain in the wall
sealing increased linearly with increasing
height. The low support of the gabions during
compaction resulted in these large horizontal
strains. Additionally, this construction tech-
nique led to an exponential increase in the
horizontal strain in the base sealing under the
gabions.
32. The vertical deformation in the wall
sealing was constant across its width due to the
smooth surface along the side walls and the
large ductility of the gabions. The di�erential
vertical settlements at maximum were
ee Z =78% (Fig. 14(b)), the horizontal strain at
maximum ee h = 5±9% (Fig. 14(a)). The
maximum extension produced a tilt of about
1´28. The horizontal strain during construction
produced an additional rotation of 28. In cross-
section II the vertical and horizontal deforma-
tions resulted in a distortion of ee g=17% at a
height of 6 m above the foundation of the
gabions. The volumetric deformation can be
calculated approximately from the inclinometer
and the sliding micrometer measurements. A
volume decrease of 5% (without volume
decrease during compaction) at maximum was
obtained in the wall sealing, implying a
decrease in hydraulic conductivity.
Comparison of the 1:1 scale tests33. With the two model tests, horizontal and
vertical, the stress±strain behaviour of possible
barrier systems has been investigated.
However, there exist di�erent conditions which
possibly lead to failure and loss of service-
ability. Generally, there are three main points
which increase the hydraulic conductivity
(a) horizontal stretching
(b) increase of volume
(c) increase of shear strain.
While (a) is the most likely e�ect for horizontal
barriers, vertical or inclined barriers might fail
by (b) and/or (c).
34. The maximum horizontal strains and
volume changes of the models and laboratory
tests performed are summarized in Table 2
together with the permeability measured on
samples both compacted before and taken after
the model tests. Without overburden (horizontal
tests), the stretching strains at which damage
occurs are much less than in an overall stress
state (0´2% (silt) to 1´3% (clay) instead of
1´0% (silt) to 5´0% (clay)). On the other hand,
laboratory tests showed that for clayey material
under volume extension up to 5´6% no sig-
ni®cant change of permeability (k=2´9 to
2´86 10710 m/s) was measured.
35. The vertical model tests show that
distortions up to 16% also do not cause an
increase in permeability for silty material. But
it should be considered that the strain condi-
tions produced a ®nal volume decrease of 6%
within the same loading procedure. So, in the
investigated system, the material can also
withstand temporary volume increase (up to
6%) without reducing the hydraulic conductiv-
ity signi®cantly.
Conclusions36. There is only scant information avail-
able in the literature and in regulations con-
cerning the deformation behaviour of soil liners
for practical applications. For example, in
German regulations, a minimum radius of
curvature of R=200 m is given for which no
deformation improvement is necessary for hor-
izontal soil liners of at least medium plasticity.8
From the large-scale tests, the limiting value of
deformation of silt is about R=70 m, corre-
sponding to the maximum radius of curvature
(b)
(a)
20
15
10
5
0
Hei
ght:
m20
15
10
5
0
Hei
ght:
m
0 2 4 6 8 10
–5 0 5 10 15
Vertical strain: %
Foundation ofthe gabions
Foundation of the gabions
Vertical line near the side wallVertical line near the body of waste
Horizontal strain: %
Side wall(rock)
Cross–section Ι
Cross–section ΙΙ
Body of waste
Fig. 14. Measured
strains versus height
for Wirmsthal
land®ll, showing:
(a) horizontal (cross
sections I + II); and
(b) vertical (cross-
section II)
222
EDELMANN ET AL.
which caused the ®rst leak. Silt of low plasti-
city already meets the requirements concerning
deformability of barrier material of medium
plasticity according to the LWA Instructions.
The barrier model with clay sustained a radius
of curvature of R=6 m without reaching a
limit state. The important di�erence in the
amount of deformation is attributed to the
di�erent plasticity of the materials. The limits
of R were measured in the model test without
overburden. These conditions are similar to
caps. The ®eld test showed values of R� 30 m
without damage under an overburden. These
conditions are similar to conditions of inter-
mediate liners.
37. The stress±strain conditions of vertical
or steep-sloped liners are characterized by the
construction detail of the barrier system. It is
obvious that if the inclined wall is rough and if
large displacements occur along the wall, the
slender wall sealing will be subject to uncon-
trolled shear stress, producing vertical cracks.
Beside the roughness of the wall, the low
normal stress on the wall also contributes to the
uncontrolled shear stress. Therefore the shear
forces along this interface must be reduced.
However, it is not necessary to have a smooth
contact surface between the wall sealing and
the leachate collection system, if a transition
zone (drainage layer) is installed.
38. The magnitudes of the total vertical and
horizontal strains in the vertical liner depend
on the sti�ness of the waste body. In the case of
a sanitary land®ll in a quarry, the principal
load case is the so-called self-weight loading.
The load transfer from the weak waste material
causes smaller additional vertical deformations.
The requirements concerning the strength of
the sealing material depend upon the height.
39. The ®lling and construction sequences
have an important in¯uence on the stability and
the deformation of the sealing system. Increas-
ing displacements can be avoided by adapting
the ®lling sequence accordingly. High compac-
tion of the MSW is recommended near the
sealing system, to provide su�cient support
and smaller lateral deformation in the wall
sealing.
40. Both vertical model tests and the ®eld
measurements con®rmed that the chosen con-
struction of the Wirmsthal barrier system with
a sealing material of high plasticity, ful®lled
the requirements. Nevertheless, a sealing
material should be compacted and installed at a
moulding water content on the wet side of
Proctor optimum, yielding densi®cation at low
stress levels and insurance against volume
change due to drying during the long-term life
of a waste deposit.
41. The investigations presented in this
paper give the possibility to perform an overall
design for horizontal, vertical and sloped dis-
posal barrier systems. The given design criteria
are stretching, bending, buckling and also
bulging. The testing equipment developed also
allows tests for the quality control of new
system designs or a combination of materials.
Nevertheless, 1:1 scale tests are very costly and
time-consuming. Therefore the results will be
evaluated by further ®nite element computa-
tions and more sophisticated element tests with
the construction materials used.
Acknowledgements42. The horizontal model test was per-
formed at the Technical University in Darm-
stadt and ®nanced by the German Research
Institution. The vertical model test was
installed at the Swiss Federal Institute of
Technology in Zurich and ®nanced by the
Research Commission and fund of the school.
The ®eld measurements in both cases were
funded by the owner of the land®lls in Asslar,
Germany and Wirmsthal, Germany. Thanks
are given to all who have supported this
extensive work, especially to the people of the
university workshops who constructed, oper-
ated and repaired the equipment with a con-
sistently high level of commitment to the
research work.
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223
MECHANICAL BEHAVIOUR
OF LANDFILL BARRIER
SYSTEMS
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Please email, fax or post your discussion contributions to the Secretary:
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224
EDELMANN ET AL.