Undrained Pore Pressure Development on Cohesive Soil in Triaxial Cyclic Loading

: Cohesive soils subjected to cyclic loading in undrained conditions respond with pore pressure generation and plastic strain accumulation. The article focus on the pore pressure development of soils tested in isotropic and anisotropic consolidation conditions. Due to the consolidation di ﬀ erences, soil response to cyclic loading is also di ﬀ erent. Analysis of the cyclic triaxial test results in terms of pore pressure development produces some indication of the relevant mechanisms at the particulate level. Test results show that the greater susceptibility to accumulate the plastic strain of cohesive soil during cyclic loading is connected with the pore pressure generation pattern. The value of excess pore pressure required to soil sample failure di ﬀ ers as a consequence of di ﬀ erent consolidation pressure and anisotropic stress state. E ﬀ ective stresses and pore pressures are the main factors that govern the soil behavior in undrained conditions. Therefore, the pore pressure generated in the ﬁrst few cycles plays a key role in the accumulation of plastic strains and constitutes the major amount of excess pore water pressure. Soil samples consolidated in the anisotropic and isotropic stress state behave di ﬀ erently responding di ﬀ erently to cyclic loading. This di ﬀ erence may impact on test results analysis and hence may change the view on soil behavior. The results of tests on isotropically and anisotropically consolidated soil samples are discussed in this paper in order to point out the main features of the cohesive soil behavior.


Introduction
The cyclic loading sources can be distinguished into two categories. The first one is natural sources as ocean waves or earthquake. The second one is the anthropogenic sources. This type of excitation is different because of the loading amplitude and the frequency [1,2]. Cyclic loading can cause rapid failure due to high level repeating stress imposed on the structure or liquefaction when certain soil conditions are met [3,4]. When the load is small enough, the repeating loading can last longer. In that case, the bearing capacity failure will not be reached but excessive settlements can occur [2,5,6]. In this case, post-construction settlements may put out of service further construction. Regarding foundations or road constructions the weakest link is subgrade soils [6]. The traffic loading is a good example of a certain choice, which geotechnical designers need to take [7][8][9]. When thick embankments are designed, the repeating loading can be transmitted to the subgrade soils, which will result in unknown settlements. The solution to this problem is to increase the embankments thickness and therefore to prevent the cyclic loads to be imposed on the subgrade soils. Nevertheless, this solution generates extra costs to road construction due to longer embankment construction and settlements of subgrade

Soil Index Properties
The cohesive soil in this study was taken from a road construction site. The cohesive soil tested in this study is typical soil, which represents primary deposits, left behind by a glacier. This type of glacial till is common for the northern and central part of Poland. The clay was recognized as one of the problematic soils due to low permeability and low bearing capacity. The soil has a brown color and is characterized by heterogenic soil diameter distribution with a dominant fraction 0.05-0.1 mm [39]. The soil is normally consolidated and often natural moisture content places it in soft rarely firm consistency. This type of soil has also a low plasticity index (10% < I P < 30%). The soil in the natural state has low to medium strength (undrained strength c u in the range 20 to 60 kPa) based on CPT (Cone Penetration Test) and DMT (Dilatometer Test) tests [40]. The index properties were established including the soil grain composition, Atterberg limits, and optimal moisture content. The results of the tests present in Table 1. The cohesive soil was recognized based on the Eurocode 7 [41,42] classification as sandy silty clay (sasiCl). Table 1. Index properties of tested sandy silty clay.

Index Properties Value
Specific gravity, G s (g/cm 3 ) 2.67 Optimal moisture content, w opt (%) 12.3 Maximal dry density, ρ d max (g/cm 3 ) 1.96 Liquid limit, w L (%) 42.0 Plasticity index, I P (%) 18.4 Clay fraction, f Cl (%) 19 Silt fraction, f Si (%) 41 Sand fraction, f Sa (%) 40 Figure 1 presents the result of monotonic triaxial tests with different confining pressures. The parameters on the figures are the deviator stress q = σ 1 − σ 3 , mean effective stress p = (σ 1 + 2σ 3 )/3, axial vertical strain ε 1 , and excess pore water pressure ∆u. On Figure 1a the effective stress paths on the p -q plane are presented. The slope of the critical state line (CSL) is given as M = 1.33. The monotonic triaxial tests results indicate the typical compacted soil behavior. This type of soil response can be called quasi-overconsolidated due to the reverse curvature of the stress path. The failure points were estimated based on the intersection between the stress path and the CSL. The deviator stress at failure q max was 46.04, 93.66, and 153.55 kPa for confining pressures of 45, 90, and 135 kPa respectively. The pore pressure presented in Figure 1c shows peak values of the pore pressure and therefore indicates the maximum axial strain ε 1, max achieved by sample when failure Appl. Sci. 2019, 9,3821 4 of 23 occurred the value of ε 1, max was 1.102%, 2.277%, and 3.439% and the maximal excess pore water pressure ∆u was 27. 39

Soil Sample Properties, Preparation, and Origin.
The soil in this study was taken from a road construction site placed in Warsaw. The depth of soil deposition was at 1 m below the ground and the soils were classified as Pleistocene moraine deposits of the Warta Glaciation.
The soil was stored and dried. The soil past used for sample preparation was in optimal moisture content conditions and the soil was then compacted with respect to the Proctor method [43]. The energy of compaction was equal to 0.59 J/cm 3 . The soil paste was compacted in a scaled two-part aluminum mold with the dimensions of a triaxial soil sample (7 cm diameter and 14 cm height). The sandy silty clay sample properties in this study are presented in Table 2. The initial void ratio e0 was constant during the undrained cyclic triaxial test and was in the range between 0.333 to 0.414. The initial density ρd of tested soils was in the range of 1.89 to 2.10 g/cm 3 .

Soil Sample Properties, Preparation, and Origin
The soil in this study was taken from a road construction site placed in Warsaw. The depth of soil deposition was at 1 m below the ground and the soils were classified as Pleistocene moraine deposits of the Warta Glaciation.
The soil was stored and dried. The soil past used for sample preparation was in optimal moisture content conditions and the soil was then compacted with respect to the Proctor method [43]. The energy of compaction was equal to 0.59 J/cm 3 . The soil paste was compacted in a scaled two-part aluminum mold with the dimensions of a triaxial soil sample (7 cm diameter and 14 cm height). The sandy silty clay sample properties in this study are presented in Table 2. The initial void ratio e 0 was constant during the undrained cyclic triaxial test and was in the range between 0.333 to 0.414. The initial density ρ d of tested soils was in the range of 1.89 to 2.10 g/cm 3 .

Test Procedure
The compacted soil was installed in triaxial apparatus and the saturation process had started. This stage of the triaxial test was performed so full saturation conditions can be achieved. The saturation step was terminated when the Skempton parameter B was equal to 0.95, which has been assumed from a technical point of view and indicates full near saturation conditions. The second stage was consolidation. The consolidation was conducted in isotropic and anisotropic stress (K 0 -consolidation) conditions. For isotropic consolidation, the stress in cell pressure remained constant and the leakage of pore water pressure was measured. The isotropic consolidation was stopped when the pore water pressure effluent was less than 5 mm 3 per five minutes.
The anisotropic consolidation set up was designed to achieve pointed effective stress of consolidation σ k0 . The sample was loaded by the deviator stress q and the radial stress during the K 0 consolidation was automatically controlled by the triaxial equipment system. The cell pressure compensated the effect of deviator stress loading.
After the consolidation step, the cyclic loading test was conducted. The cyclic deviator stress components were the maximal and minimal deviator stress denoted as q max and q min respectively and two supplemental values of the cyclic deviator stress: Deviator stress amplitude q a and deviator stress median q m . The cyclic triaxial test program presents Table 3. The soil specimens were tested in the constant frequency of loading equal to 1 Hz. The loading wave-form was the semi-sin wave type. The number of cycles was from 10,000 to 50,000 cycles. The tests were conducted in different effective confining pressure levels. The cyclic stress ratio is taken as the ratio of the maximum cyclic deviator stress q max to the initial effective confining pressure σ 3 . The test equipment was the cyclic triaxial apparatus-an electrodynamical system produced by GDS Instruments. The cyclic load was applied by the servo-loading system. The pressures in this study were applied by the oil pressure system. This kind of triaxial apparatus was equipped with a real-time data acquisition system, which enables long term cyclic loading.

Results and Discussion
Test results were discussed separately in order to explain the phenomena that occurred during cyclic loading. The discussion concerns the pore pressure behavior, axial strain accumulation, the deviator stress-axial strain characteristics, and the stress paths. The second part of this chapter will discuss the comparison between the isotropic and anisotropically (K 0 ) consolidated samples.

Isotropically and K 0 Consolidated Samples Test Results
On Figure 2 the undrained cyclic triaxial test results for sample 1.1 are presented. The isotropic confining pressure was equal to 45 kPa. The soil sample was loaded with the deviator stress q, which their components were as follows q m = 39.5 kPa and q a = 4.1 kPa. The soil response to such a loading program could be divided into three stages. The first one is the first loading cycle. In this stage, the soil is accumulating a high amount of permanent strain, which is accompanied by a high generation of excess pore water pressure. The stress path (Figure 2e) rises to planned deviator stress level and mean effective stress p starts to move towards the deviator stress axis, which indicates a decrease of radial stress due to the mobilization of excess pore water pressure. After the first cycle, the second type of soil response began. The pore pressure rose to a local maximal value equal to around 17 kPa in the 4th cycle ( Figure 1a) and then dropped to 15 kPa in the 11th cycle. After this circumstance, the pore pressure rose with decreasing increment. During this phase, the permanent strains were also accumulated. This phase ended around the 350th cycle. In the first cycle phase and in the second one, most of the permanent strains occurred. The excess pore pressure reached most of its value in these two stages.
The second phase characterized with decreasing strain and excess pore water pressure value increment. Nevertheless, permanent strain accumulation and the pore pressure build-up process dependence are more complex and needs to be investigated further. This can be easily noticed by the Figure 2b,c analysis. Strain accumulation lasted longer than the pore pressure build up or the pore After the first cycle, the second type of soil response began. The pore pressure rose to a local maximal value equal to around 17 kPa in the 4th cycle ( Figure 1a) and then dropped to 15 kPa in the 11th cycle. After this circumstance, the pore pressure rose with decreasing increment. During this phase, the permanent strains were also accumulated. This phase ended around the 350th cycle. In the first cycle phase and in the second one, most of the permanent strains occurred. The excess pore pressure reached most of its value in these two stages.
The second phase characterized with decreasing strain and excess pore water pressure value increment. Nevertheless, permanent strain accumulation and the pore pressure build-up process dependence are more complex and needs to be investigated further. This can be easily noticed by the Figure 2b,c analysis. Strain accumulation lasted longer than the pore pressure build up or the pore pressure increment slowed down faster than permanent strain accumulation. On Figure 2a after the local minimum, stabilization of the pore pressure increase was observed to a certain point. When axial strain reached a value of approximately 0.5% (about the 350th cycle), the pore pressure increment had a constant value when related to the axial strain.
The last phase was the long term loading phase. In this stage, the pore pressure, as well as the permanent strain, rose with constant increment. The soil reached a stable response to cyclic loading. In this study, 20,000 cycles were applied. The excess pore water pressure was rising slightly between cycle 350 and the last cycle.
The cyclic triaxial test results in isotropic consolidation conditions where effective confining pressure was equal to 90 kPa present in Figure 3. The soil in this test had initially the void ratio equal to 0.345, which represents a more compacted sample in comparison to the previous test sample. The cyclic loading performed as well as in the previous test high pore pressure and permanent strain accumulation in the first cycle. Nevertheless, excess pore water pressure reached roughly 11 kPa (17 kPa in the previous test). Unlike the previous test the axial strain increment was greater than in the previous step (0.65% in test 1.2 and 0.16% in test 1.1). This difference was clearly caused by the difference between the initial void ratio and in the radial effective confining pressure. In the second stage of loading, the pore pressure rose in a greater amount than in the previous test.
Appl. Sci. 2019, 9, x 7 of 23 pressure increment slowed down faster than permanent strain accumulation. On Figure 2a after the local minimum, stabilization of the pore pressure increase was observed to a certain point. When axial strain reached a value of approximately 0.5% (about the 350th cycle), the pore pressure increment had a constant value when related to the axial strain. The last phase was the long term loading phase. In this stage, the pore pressure, as well as the permanent strain, rose with constant increment. The soil reached a stable response to cyclic loading. In this study, 20,000 cycles were applied. The excess pore water pressure was rising slightly between cycle 350 and the last cycle.
The cyclic triaxial test results in isotropic consolidation conditions where effective confining pressure was equal to 90 kPa present in Figure 3. The soil in this test had initially the void ratio equal to 0.345, which represents a more compacted sample in comparison to the previous test sample. The cyclic loading performed as well as in the previous test high pore pressure and permanent strain accumulation in the first cycle. Nevertheless, excess pore water pressure reached roughly 11 kPa (17 kPa in the previous test). Unlike the previous test the axial strain increment was greater than in the previous step (0.65% in test 1.2 and 0.16% in test 1.1). This difference was clearly caused by the difference between the initial void ratio and in the radial effective confining pressure. In the second stage of loading, the pore pressure rose in a greater amount than in the previous test.  presents test results for the soil sample under a confining pressure equal to 135 kPa and an initial void ratio e 0 equal to 0.412. In the first cycle stage, the soil response was stiffer than in test 1.2 but pore pressure rose to 11.5 kPa, which was close to the response observed in test 1.2. The same conclusion could be formed, when the excess pore water pressure versus axial strain plots (Figures 3a and 4a) were compared. and under the isotropic consolidation, initial void ratio e0 = 0.345-sample 1.2: (a) Excess pore water pressure versus vertical strain characteristic, (b) excess pore water pressure characteristic versus number of cycles, (c) vertical strain characteristic versus number of cycle, (d) deviator stress-vertical strain relationship, and (e) the deviator stress-mean effective stress relationship (red color-last 10 cycles; arrow color-violet: Saturation phase, green: Consolidation phase, orange: First cycle of cyclic loading, blue: Cyclic loading program). Figure 4 presents test results for the soil sample under a confining pressure equal to 135 kPa and an initial void ratio e0 equal to 0.412. In the first cycle stage, the soil response was stiffer than in test 1.2 but pore pressure rose to 11.5 kPa, which was close to the response observed in test 1.2. The same conclusion could be formed, when the excess pore water pressure versus axial strain plots (Figures 3a and 4a) were compared.  In the second stage of the soil response, the pore pressure rose as well as the axial strain in the same pattern. The permanent strain accumulation to ∆u characteristics was almost linear in both cases, which means, that for the same amount of pore pressure increment, the same amount of accumulated plastic strain was observed. Nevertheless, the magnitude of this phenomenon was different in each stage. In both cases, the limit between the second and third stage of the soil response could not be distinguished. The excess pore water pressure level and its increment rise with initial effective confining pressure growth. The stress paths in all cases moved towards the deviator stress axis, which indicates undrained conditions.
On Figures 5-9, results of the cyclic triaxial test in K 0 consolidation conditions are presented. The soil response to cyclic loading differed when compared to previous tests. The excess pore water pressure in test 2.1 rose rapidly, which was accompanied by moderate axial strain accumulation. When the ∆u increment started to decrease, the permanent axial strain began to develop.
That process of the soil reaction to cyclic loading indicates that the pore pressure triggered plastic strain accumulation. This was true since the excess pore pressure decreased the effective stress in the soil skeleton and therefore is weakening the soil contacts. During test 2.1 excess pore water pressure reached a maximum value equal to 35 kPa after around 2500 cycles of loading and then slowly decreased to 33 kPa after 3000 cycles. The excess pore water pressure remained after the previous event at a constant level and equaled 32 kPa up to 33 kPa.
The soil response can be divided into two stages, the pre-maximal excess pore water pressure stage, where rapid pore pressure generation and permanent strain accumulation was observed, and the second stage-the post-maximal pore pressure stage where permanent axial strains suddenly stopped and pore pressure decreased to a constant level.
It is clear that the decrease of pore pressure would result in an increase of effective mean stress and therefore would increase the soil stiffness and the permanent strain accumulation would rapidly decrease. The reason for this phenomenon is the critical soil state, which was achieved during the first part of cyclic loading. The soil accumulated 4% of axial permanent strain during the first 2500 cycles of loading. The pore water pressure development has led to soil failure. After the failure, the pore pressure dropped and therefore, the soil was able to sustain further loading. Furthermore, almost a constant high level of pore water pressure was observed, which was accompanied by a slight permanent strain accumulation. Figure 5e presents the abovementioned behavior. The stress paths moved towards the deviator stress axis and when the stress state reached the soil critical state, pore pressure decreased, and the stress path turned around.
On Figure 6 triaxial test results on the K 0 consolidated sandy silty clay sample is presented. The K 0 stress state was equal to 0.71, which was close to the previous K 0 stress state for sample 2.1, which was equal to 0.67. The initial void ratio in the case of sample 2.2 was around 0.07 greater than in the case of the 2.1 sample and was equal to 0.399. The type of loading in this study was a sin wave as in previous cases but it was performed in another manner. The soil was loaded with the deviator stress, which was oscillating around the point where the consolidation phase was terminated (q m was on the deviator stress level reached after K 0 consolidation). For example, the 2.1 test was performed in such a manner where the minimum deviator stress q min was on the deviator stress level after consolidation. In the first cycles, negative excess pore water pressure was observed. After 10,000 cycles the excess pore pressure had raised to 30 kPa. The pore water pressure was building up with a decrease of its increment. This type of soil response caused almost no plastic strains (0.134% after 10,000 cycles). It seems that the type of loading has a great impact on the K 0 consolidation samples response. The soil in which the negative pressure occurred would suffer much lesser plastic strains. This was a result of another pore pressure generation model. In the previous tests of isotropically consolidated samples, the pore pressure rose rapidly in the first few cycles, this was accompanied by plastic strain accumulation. Sample 2.1. also generated excess pore water pressure but was much faster than in the case of sample 2.2, which was the reason why the plastic strains were accumulated with a much slower rate.
Appl. Sci. 2019, 9, x 10 of 23 case of sample 2.2, which was the reason why the plastic strains were accumulated with a much slower rate. A similar response to cyclic loading can be observed in test 2.5 where the sample was consolidated to σ'3 equal to 44.9 kPa. The soil was loaded with 13.3 kPa deviator stress amplitude and the excess plastic strain was observed. The pore pressure, in this case, had not reached maximal value, which indicates no failure in this test. The soil tended to stabilize its response to cyclic loading. The pore pressure after 5000 cycles increased at a slower rate and plastic strain as well accumulated with a decreasing rate. The excess pore water pressure had greater amplitude than in test 2.1 but this phenomenon was caused by greater deviator stress amplitude qa. Samples 2.3 and 2.4 (Figures 7 and A similar response to cyclic loading can be observed in test 2.5 where the sample was consolidated to σ 3 equal to 44.9 kPa. The soil was loaded with 13.3 kPa deviator stress amplitude and the excess plastic strain was observed. The pore pressure, in this case, had not reached maximal value, which indicates no failure in this test. The soil tended to stabilize its response to cyclic loading. The pore pressure after 5000 cycles increased at a slower rate and plastic strain as well accumulated with a decreasing rate. The excess pore water pressure had greater amplitude than in test 2.1 but this phenomenon was caused by greater deviator stress amplitude q a . Samples 2.3 and 2.4 (Figures 7 and 8) were consolidated in K 0 stress conditions and with a confining pressure σ 3 equal to 139.7 and 94.2 kPa respectively. The pore pressure response to cyclic loading in the case of sample 2.3 (q a equal to 10.4 kPa) was higher than in the case of sample 2.4 (q a equal to 15.8 kPa). The cause of this phenomenon was the lower initial void ratio e 0 in the case of sample 2.4 (e 0 = 0.276) than in sample 2.3 (e 0 = 0.379). The greater density of sample 2.4 resulted in lower pore pressure generation. Nevertheless, plastic strain accumulated in sample 2.4 with a higher rate than in sample 2.3. In sample 2.2 (on Figure 6 with e 0 = 0.399 σ 3 = 125.0 kPa, and q a = 13.5 kPa), the plastic strain accumulation was close to what could be observed in the case of sample 2.3.   The axial strain, which was measured in this study, could be divided into two categories based on the plastic strain accumulation rate. The first one is steady exponential growth in which, the plastic strain increment decreases with each cycle. In this case, the soil might suffer extensive deformation due to accumulated plastic strains after numerous cycles. This type of response was observed in samples 2.2, 2.3, and 2.4. The second type of plastic strain development represents samples 2.1 and 2.5 where the extensive plastic strain was accumulated in the first phase of cyclic loading due to the imposed high value of the deviator stress. After a few thousands repetitions, the steady response of the cohesive soil was observed, which characterized the lower rate of plastic strain accumulation. The axial strain, which was measured in this study, could be divided into two categories based on the plastic strain accumulation rate. The first one is steady exponential growth in which, the plastic strain increment decreases with each cycle. In this case, the soil might suffer extensive deformation due to accumulated plastic strains after numerous cycles. This type of response was observed in samples 2. The pore pressure response to cyclic loading was also influenced by the deviator stress value. The samples that failed or were close to failing (2.1 and 2.5) generated higher pore pressure in the first 2000 cycles than the other three K0-consolidated samples. Nevertheless, here could be also seen that after reaching maximum value by excess pore water pressure the increment was much lower than in samples 2.2 to 2.4. The pore pressure response to cyclic loading was also influenced by the deviator stress value. The samples that failed or were close to failing (2.1 and 2.5) generated higher pore pressure in the first 2000 cycles than the other three K 0 -consolidated samples. Nevertheless, here could be also seen that after reaching maximum value by excess pore water pressure the increment was much lower than in samples 2.2 to 2.4.

The Effect of Consolidation on the Soil Response to Cyclic Loading
For the purpose of establishing the difference between the soil response to cyclic loading for samples consolidated in isotropic and K0 conditions, the plots of distinct cycles are presented in Figure 10. Figure 10a presents the cycles 1000 and 20,000 where the Δu-ε characteristic for one cycle of isotropically consolidated sample is presented. The plot shows, that the hysteresis curve had the same shape. The 1000 cycle was characterized by a hysteresis curve in which the area of the hysteresis and its inclination changed. The pattern of hysteresis curve evolution was similar for tests 1.1 and

The Effect of Consolidation on the Soil Response to Cyclic Loading
For the purpose of establishing the difference between the soil response to cyclic loading for samples consolidated in isotropic and K 0 conditions, the plots of distinct cycles are presented in Figure 10. Figure 10a presents the cycles 1000 and 20,000 where the ∆u-ε characteristic for one cycle of isotropically consolidated sample is presented. The plot shows, that the hysteresis curve had the same shape. The 1000 cycle was characterized by a hysteresis curve in which the area of the hysteresis and its inclination changed. The pattern of hysteresis curve evolution was similar for tests 1.1 and 1.3. The inclination and the area of the hysteresis curve rose in both cases. The different responses could be observed in the case of sample 1.2 wherein cycle 20,000 the inclination, as well as the area, was smaller. The unloading process in this test showed that sample tended to decrease excess pore water pressure much faster than the recovering of strain. This difference of the response to cyclic loading was caused by the initial void ratio difference since there was no distinct difference in deviator stress conditions. The impact of the initial void ratio could be seen in terms of the generated excess pore water pressure in one cycle. The excess pore water pressure in the case of tests 1.1 and 1.3 had risen up to 1.8 and 1.7 kPa. In the case of sample 1.2, the excess pore water pressure built up to 1.1 kPa, which was less when comparing the amount of generated pore pressure. On the other hand, the axial strain in one cycle caused by cyclic loading seemed to be independent of the initial void ratio. The axial strain in one cycle was equal to 0.0216%, 0.0177%, and 0.0146% respectively for the initial consolidation pressure σ 3,0 equal to 45 kPa, 90 kPa, and 135 kPa and seemed that the σ 3,0 was the governing factor in this phenomena.
Appl. Sci. 2019, 9, x 15 of 23 1.3. The inclination and the area of the hysteresis curve rose in both cases. The different responses could be observed in the case of sample 1.2 wherein cycle 20,000 the inclination, as well as the area, was smaller. The unloading process in this test showed that sample tended to decrease excess pore water pressure much faster than the recovering of strain. This difference of the response to cyclic loading was caused by the initial void ratio difference since there was no distinct difference in deviator stress conditions. The impact of the initial void ratio could be seen in terms of the generated excess pore water pressure in one cycle. The excess pore water pressure in the case of tests 1.1 and 1.3 had risen up to 1.8 and 1.7 kPa. In the case of sample 1.2, the excess pore water pressure built up to 1.1 kPa, which was less when comparing the amount of generated pore pressure. On the other hand, the axial strain in one cycle caused by cyclic loading seemed to be independent of the initial void ratio. The axial strain in one cycle was equal to 0.0216%, 0.0177%, and 0.0146% respectively for the initial consolidation pressure σ'3,0 equal to 45 kPa, 90 kPa, and 135 kPa and seemed that the σ'3,0 was the governing factor in this phenomena. The excess pore water pressure in the case of K0 consolidated samples had different characteristics. The Δu in one cycle was greater for test 2.2 where the deviator stress parameters were smaller in terms of the stress median and greater in terms of deviator stress amplitude. Test 2.2 was characterized by the excess pore water pressure equal to 4.5 kPa after 10,000 cycles. The same excess pore water pressure value was observed in the case of sample 2.5. The value of Δu/qa ratio was equal to 0.257, 0.333, 0.240, 0.190, and 0.338 respectively. The difference between the ratios was caused by different initial void ratios and different median levels of deviator stress. The impact of e0 shows that the bigger the initial void ratio value was the greater value of the Δu/qa ratio in one cycle would be. Although the deviator stress amplitude was greater in the case of sample 2.2, while the qm value was otherwise. Another way of loading, in the case of sample 2.2 results in different characteristics of the excess pore water pressure generation. The excess pore water pressure in the case of K 0 consolidated samples had different characteristics. The ∆u in one cycle was greater for test 2.2 where the deviator stress parameters were smaller in terms of the stress median and greater in terms of deviator stress amplitude. Test 2.2 was characterized by the excess pore water pressure equal to 4.5 kPa after 10,000 cycles. The same excess pore water pressure value was observed in the case of sample 2.5. The value of ∆u/q a ratio was equal to 0.257, 0.333, 0.240, 0.190, and 0.338 respectively. The difference between the ratios was caused by different initial void ratios and different median levels of deviator stress. The impact of e 0 shows that the bigger the initial void ratio value was the greater value of the ∆u/q a ratio in one cycle would be. Although the deviator stress amplitude was greater in the case of sample 2.2, while the q m value was otherwise. Another way of loading, in the case of sample 2.2 results in different characteristics of the excess pore water pressure generation.
The excess pore water pressure in cycle 1000 had different characteristics than the cycle observed in cycle 20,000 or 10,000. The cycle in the case of sample 2.1 and 2.3 had a small area and greater inclination than in the last cycle of loading. Sample 2.2 and 2.5 were characterized by high excess pore water pressure generation, the big area of the hysteresis curve in comparison to previous tests and the same inclination after 10,000 cycles of loading. The same phenomena can be seen in sample 2.4's response to cyclic loading. The lesser pore water pressure value might be caused by a low initial void ratio. In Figure 11, the comparison of laws cycle of loading for excess pore water pressure and the deviator stress increment in one cycle was presented. The tests on the isotropically consolidated samples showed that for the same initial void ratio, the excess pore water pressure generated in one cycle had the same value for equal stress conditions. Sample 1.2, which was more compact, had lower generated excess pore water pressure in comparison to deviator stress conditions that corresponds to the previously observed phenomena. The ∆u/q max ratio was equal to 0.195, 0.122, and 0.200 respectively.
The K 0 -consolidated samples behaved in a similar way. Sample 2.1 with an e 0 equal to 0.333 had the ∆u/q max ratio equal to 0.108, which corresponds to sample 1.2 where e 0 was equal to 0.345. The sample 2.2 with an initial void ratio equal to 0.399 had the ∆u/2q a ratio equal to 0.170. This relationship was almost linear for all five samples. Based on this test the conclusion could be formed, the excess pore water pressure in one cycle in long-term cyclic loading test depended on the deviator stress amplitude and the initial void ratio. This indicates that the consolidation type would not impact on this characteristic. Nevertheless, the differences could be seen in the inclination of the stress-strain and excess pore water pressure-strain characteristics. The excess pore water pressure in cycle 1000 had different characteristics than the cycle observed in cycle 20,000 or 10,000. The cycle in the case of sample 2.1 and 2.3 had a small area and greater inclination than in the last cycle of loading. Sample 2.2 and 2.5 were characterized by high excess pore water pressure generation, the big area of the hysteresis curve in comparison to previous tests and the same inclination after 10,000 cycles of loading. The same phenomena can be seen in sample 2.4's response to cyclic loading. The lesser pore water pressure value might be caused by a low initial void ratio. In Figure 11, the comparison of laws cycle of loading for excess pore water pressure and the deviator stress increment in one cycle was presented. The tests on the isotropically consolidated samples showed that for the same initial void ratio, the excess pore water pressure generated in one cycle had the same value for equal stress conditions. Sample 1.2, which was more compact, had lower generated excess pore water pressure in comparison to deviator stress conditions that corresponds to the previously observed phenomena. The Δu/qmax ratio was equal to 0.195, 0.122, and 0.200 respectively.
The K0-consolidated samples behaved in a similar way. Sample 2.1 with an e0 equal to 0.333 had the Δu/qmax ratio equal to 0.108, which corresponds to sample 1.2 where e0 was equal to 0.345. The sample 2.2 with an initial void ratio equal to 0.399 had the Δu/2qa ratio equal to 0.170. This relationship was almost linear for all five samples. Based on this test the conclusion could be formed, the excess pore water pressure in one cycle in long-term cyclic loading test depended on the deviator stress amplitude and the initial void ratio. This indicates that the consolidation type would not impact on this characteristic. Nevertheless, the differences could be seen in the inclination of the stress-strain and excess pore water pressure-strain characteristics. For K0-consolidated samples' Δu/qmax ratio had a linear relationship with qm/qa, which indicates that the excess pore water pressure value in one cycle impacted the deviator stress characteristics. For K 0 -consolidated samples' ∆u/q max ratio had a linear relationship with q m /q a , which indicates that the excess pore water pressure value in one cycle impacted the deviator stress characteristics.
The inclination of the hysteresis loop can be described by the modulus conception. The stress-strain characteristics in cyclic loading are often explained with the resilient modulus definition. The resilient modulus M r is a quotient of cyclic stress and resilient strain and for the purpose of this study can be defined as: The deviator stress difference is the cyclic stress in one cycle. Therefore, the cyclic stress can be defined as a double deviator stress amplitude in one cycle. The resilient strain is accordingly the maximum and minimum strain observed in one cycle. Another type of soil modulus that can help to understand how excess pore water pressure impacts on the soil stiffness in one cycle is the excess pore water pressure modulus M ∆u , which can be defined as the quotient of excess pore water pressure in one cycle to resilient strain: The presented relationship between strain and stress components can be used for the evaluation of the hysteresis curve inclination change. On Figure 12 the resilient modulus and excess pore water pressure modulus for isotropically consolidated samples are presented. For the sample consolidated in σ 3 equal to 45 kPa, the resilient modulus characteristic was very similar to the excess pore water pressure modulus. The M r value first rose and then around cycle 50 reached its maximum value. The M ∆u value had a similar characteristic, although the maximum value was achieved around cycle 40. In the case of samples 1. The inclination of the hysteresis loop can be described by the modulus conception. The stressstrain characteristics in cyclic loading are often explained with the resilient modulus definition. The resilient modulus Mr is a quotient of cyclic stress and resilient strain and for the purpose of this study can be defined as: The deviator stress difference is the cyclic stress in one cycle. Therefore, the cyclic stress can be defined as a double deviator stress amplitude in one cycle. The resilient strain is accordingly the maximum and minimum strain observed in one cycle. Another type of soil modulus that can help to understand how excess pore water pressure impacts on the soil stiffness in one cycle is the excess pore water pressure modulus MΔu, which can be defined as the quotient of excess pore water pressure in one cycle to resilient strain: The presented relationship between strain and stress components can be used for the evaluation of the hysteresis curve inclination change. On Figure 12 the resilient modulus and excess pore water pressure modulus for isotropically consolidated samples are presented. For the sample consolidated in σ'3 equal to 45 kPa, the resilient modulus characteristic was very similar to the excess pore water pressure modulus. The Mr value first rose and then around cycle 50 reached its maximum value. The MΔu value had a similar characteristic, although the maximum value was achieved around cycle 40. In the case of samples 1. The excess pore water modulus followed the same pattern. After reaching the maximal value, MΔu decreased, this characteristic was linear in the semi-logarithmic after cycle 100 in all three cases.
On Figure 13 results of Mr and MΔu calculations for K0 consolidated samples are presented. The modulus characteristics were different from the characteristics that were observed in the case of the samples consolidated in an isotropic manner. Both modulus values first rose to around the 10th cycle and then started to decrease. When the local minimum was reached in cycle 800 for sample 2.1 and in the 500th cycle for sample 2.2 the soil resilient modulus started to increase. The MΔu followed the same pattern but it preceded the Mr value change. This is helpful information when performing the stiffness change forecasting. The hardening process, which is indicated by the resilient modulus growth, was in both cases going to end. The question was if in example test 2.2 the resilient modulus would decrease again.
Similar phenomena could be observed in the case of sample 2.5 where after numerous cycles, the soil resilient modulus was reaching its lowest value (around cycle 3000) and then rose again. During the test 2.3 the plastic strain rate was the lowest. Therefore, the modulus characteristic was less obvious than in the previously mentioned test. Nevertheless, two local minima of modulus value could be observed. Test 2.4 in which the CSR value was the highest shows that the resilient modulus, as well as the excess pore water pressure modulus, decreased. The local characteristic change might be spotted around cycle 5000 but there was no stiffness increase after this event. Samples with high CSR value had a similar pattern of responding to cyclic loading.
We can see that the MΔu value started to decrease, which meant that for the same amount of strain the pore pressure growth was smaller than in previous cycles and which meant that the effective stresses would increase. This might result in another phase of softening or might indicate that the soil achieved some state of equilibrium. Nevertheless, it is worth to note that the previous phase of softening and hardening took around 1000 cycles and now the repeating of the process would take many more cycles to occur.
(a) The excess pore water modulus followed the same pattern. After reaching the maximal value, M ∆u decreased, this characteristic was linear in the semi-logarithmic after cycle 100 in all three cases.
On Figure 13 results of M r and M ∆u calculations for K 0 consolidated samples are presented. The modulus characteristics were different from the characteristics that were observed in the case of the samples consolidated in an isotropic manner. Both modulus values first rose to around the 10th cycle and then started to decrease. When the local minimum was reached in cycle 800 for sample 2.1 and in the 500th cycle for sample 2.2 the soil resilient modulus started to increase. The M ∆u followed the same pattern but it preceded the M r value change. This is helpful information when performing the stiffness change forecasting. The hardening process, which is indicated by the resilient modulus growth, was in both cases going to end. The question was if in example test 2.2 the resilient modulus would decrease again.
Similar phenomena could be observed in the case of sample 2.5 where after numerous cycles, the soil resilient modulus was reaching its lowest value (around cycle 3000) and then rose again. During the test 2.3 the plastic strain rate was the lowest. Therefore, the modulus characteristic was less obvious than in the previously mentioned test. Nevertheless, two local minima of modulus value could be observed. Test 2.4 in which the CSR value was the highest shows that the resilient modulus, as well as the excess pore water pressure modulus, decreased. The local characteristic change might be spotted around cycle 5000 but there was no stiffness increase after this event. Samples with high CSR value had a similar pattern of responding to cyclic loading.
We can see that the M ∆u value started to decrease, which meant that for the same amount of strain the pore pressure growth was smaller than in previous cycles and which meant that the effective stresses would increase. This might result in another phase of softening or might indicate that the soil achieved some state of equilibrium. Nevertheless, it is worth to note that the previous phase of softening and hardening took around 1000 cycles and now the repeating of the process would take many more cycles to occur. The excess pore water modulus followed the same pattern. After reaching the maximal value, MΔu decreased, this characteristic was linear in the semi-logarithmic after cycle 100 in all three cases.
On Figure 13 results of Mr and MΔu calculations for K0 consolidated samples are presented. The modulus characteristics were different from the characteristics that were observed in the case of the samples consolidated in an isotropic manner. Both modulus values first rose to around the 10th cycle and then started to decrease. When the local minimum was reached in cycle 800 for sample 2.1 and in the 500th cycle for sample 2.2 the soil resilient modulus started to increase. The MΔu followed the same pattern but it preceded the Mr value change. This is helpful information when performing the stiffness change forecasting. The hardening process, which is indicated by the resilient modulus growth, was in both cases going to end. The question was if in example test 2.2 the resilient modulus would decrease again.
Similar phenomena could be observed in the case of sample 2.5 where after numerous cycles, the soil resilient modulus was reaching its lowest value (around cycle 3000) and then rose again. During the test 2.3 the plastic strain rate was the lowest. Therefore, the modulus characteristic was less obvious than in the previously mentioned test. Nevertheless, two local minima of modulus value could be observed. Test 2.4 in which the CSR value was the highest shows that the resilient modulus, as well as the excess pore water pressure modulus, decreased. The local characteristic change might be spotted around cycle 5000 but there was no stiffness increase after this event. Samples with high CSR value had a similar pattern of responding to cyclic loading.
We can see that the MΔu value started to decrease, which meant that for the same amount of strain the pore pressure growth was smaller than in previous cycles and which meant that the effective stresses would increase. This might result in another phase of softening or might indicate that the soil achieved some state of equilibrium. Nevertheless, it is worth to note that the previous phase of softening and hardening took around 1000 cycles and now the repeating of the process would take many more cycles to occur.
(a) The pore pressure build-up based on stress-controlled cyclic stress can be analyzed based on the empirical models. This model is able to analyze excess pore water pressure with the number of cycles to a certain event, which in non-cohesive soils is liquefaction. In the case of cohesive soils, the pore pressure analysis can be conducted to maximal pore pressure occurrence. The parameter that governs this analysis is pore pressure ratio, which can be presented as: The pore pressure build-up based on stress-controlled cyclic stress can be analyzed based on the empirical models. This model is able to analyze excess pore water pressure with the number of cycles to a certain event, which in non-cohesive soils is liquefaction. In the case of cohesive soils, the pore pressure analysis can be conducted to maximal pore pressure occurrence. The parameter that governs this analysis is pore pressure ratio, which can be presented as: where the ∆u max is the maximum pore pressure in one cycle. The pore pressure empirical models were developed over the years. One of the best known is the pore pressure model developed by Seed et al. [44], which is defined as follows: where the N/N L is the cycle ratio, β is the empirical parameter, and N L is the last cycle analyzed in this model. On Figure 14 the results of the calculations are presented for K 0 -consolidated samples.
Appl. Sci. 2019, 9, x 20 of 23 where the Δumax is the maximum pore pressure in one cycle. The pore pressure empirical models were developed over the years. One of the best known is the pore pressure model developed by Seed et al. [44], which is defined as follows: where the N/NL is the cycle ratio, β is the empirical parameter, and NL is the last cycle analyzed in this model. On Figure 14 the results of the calculations are presented for K0-consolidated samples. The pore pressure ratio for K0-consolidated samples had similar characteristics. The pore pressure ratio rose to 0.7-0.8 of the maximum value in half of the cycle ratio. In comparison to noncohesive soils, presented characteristics rose rapidly towards ru = 1 when the cycle ratio was higher than 0.9. Nevertheless when N/NL value was equal to 0.5 the pore pressure ratio was equal to 0.4-0.6 [38][39][40][41]. An attempt to fit the seed model was made as well, the β parameter, in this case, was equal to 3.0.

Conclusions
In this article, the cyclic loading of the compacted silty sandy clay was performed. The soil samples were consolidated in two different manners. The isotropic and anisotropic (K0) consolidation impacts on soil response to repeated loading. The tested soil stress history was different from the previously tested ones due to compaction in optimum moisture content. Conducted tests were in a stress-controlled manner and a minimum of 10,000 cycles was performed to capture soil response to cyclic loading in undrained conditions. This type of test is preferable when pore pressure characterization is the focus of the tests.
Cohesive soil samples consolidated in isotropic test conditions, behaved abruptly to cyclic loading in the first cycle. The deviator stress caused rapid pore pressure generation and permanent strain generation. The first cycle showed a more severe impact on isotropically consolidated samples. The stress-controlled triaxial tests performed by Yasuchara et al. [45] shows that isotropically consolidated samples developed higher pore pressure than anisotropically consolidated samples. Nevertheless, the soil in this study was Ariake clay with an IP equal to 58%. The compacted sandy silty clay soil tested in this study behaved differently. The response to cyclic loading was more dependent on the CSR than on the consolidation method.
The cohesive soil response in isotropic consolidation conditions could be divided into three stages. The first one is the above mentioned, the first cycle, the second one is the intermediate zone, and the third one is the long term response. This type of behavior was observed in the sample with the highest tested CSR. Samples tested in higher CSR that had a two-step response to cyclic loading were compared to test 1.1, where no intermediate zone was observed. The pore pressure ratio for K 0 -consolidated samples had similar characteristics. The pore pressure ratio rose to 0.7-0.8 of the maximum value in half of the cycle ratio. In comparison to non-cohesive soils, presented characteristics rose rapidly towards r u = 1 when the cycle ratio was higher than 0.9. Nevertheless when N/N L value was equal to 0.5 the pore pressure ratio was equal to 0.4-0.6 [38][39][40][41]. An attempt to fit the seed model was made as well, the β parameter, in this case, was equal to 3.0.

Conclusions
In this article, the cyclic loading of the compacted silty sandy clay was performed. The soil samples were consolidated in two different manners. The isotropic and anisotropic (K 0 ) consolidation impacts on soil response to repeated loading. The tested soil stress history was different from the previously tested ones due to compaction in optimum moisture content. Conducted tests were in a stress-controlled manner and a minimum of 10,000 cycles was performed to capture soil response to cyclic loading in undrained conditions. This type of test is preferable when pore pressure characterization is the focus of the tests.
Cohesive soil samples consolidated in isotropic test conditions, behaved abruptly to cyclic loading in the first cycle. The deviator stress caused rapid pore pressure generation and permanent strain generation. The first cycle showed a more severe impact on isotropically consolidated samples. The stress-controlled triaxial tests performed by Yasuchara et al. [45] shows that isotropically consolidated samples developed higher pore pressure than anisotropically consolidated samples. Nevertheless, the soil in this study was Ariake clay with an I P equal to 58%. The compacted sandy silty clay soil tested in this study behaved differently. The response to cyclic loading was more dependent on the CSR than on the consolidation method.
The cohesive soil response in isotropic consolidation conditions could be divided into three stages. The first one is the above mentioned, the first cycle, the second one is the intermediate zone, and the third one is the long term response. This type of behavior was observed in the sample with the highest tested CSR. Samples tested in higher CSR that had a two-step response to cyclic loading were compared to test 1.1, where no intermediate zone was observed.
The intermediate zone is characterized by the decrease of the permanent strain accumulation magnitude as well as by the decrease of pore pressure increment in each cycle. As a result, the excess pore water pressure generation and plastic strain accumulation weaken in each cycle. This behavior is complex and no direct connection between this to phenomena can be established.
The third phase is characteristic of the long term cyclic loading. In this phase, the tendency observed in the previous stage is continued. Nevertheless, the changes in pore pressure and sample deformation may not be observed in one cycle but they might occur after several cycles. It means that in one cycle no plastic strain is observed. In this type of soil response, the effect of cyclic loading is fully embraced by the sample. The set conditions were established.
The third phase begins in the first 500 cycles. The long term pore pressure response to cyclic loading shows that the soil had reached a steady state in which the excess pore water pressure remains on the same level and changes slightly during loading.
The impact of the initial void ratio on pore pressure was recognized. High e 0 value caused a higher generation of pore water pressure.
The K 0 consolidated samples behaved differently to cyclic loading in terms of plastic strain accumulation and pore pressure development. The excess pore water pressure in the test performed with the same loading pattern as in the case of isotropic consolidation it rose rapidly in the first few hundred cycles. When the ∆u characteristic started to decrease, the permanent axial strain began to develop, which could be explained by the fact that the excess pore pressure decreased the effective stress in the soil skeleton and therefore was weakening soil contacts.
It was found that the type of loading had a great impact on K 0 consolidation samples' response. The soil in which the negative pressure occurred in the first cycles of loading would suffer much lesser plastic strains. This was the result of another pore pressure generation model. The isotropically consolidated samples generated pore pressure rapidly in the first few cycles, which was accompanied by plastic strain accumulation. The K 0 consolidated soil also generated excess pore water pressure but much faster than in the case of K 0 consolidated soil loaded with another manner, which was the reason why the plastic strains were accumulated with a much slower rate.
To establish the difference between the soil response to cyclic loading for soil consolidated in isotropic and K 0 conditions the hysteresis curve analysis for a distinct cycle was performed. The ∆u/q max ratio was dependent on the initial void ratio in both cases of consolidation techniques. Nevertheless, the differences could be seen in the inclination of the stress-strain and excess pore water pressure-strain characteristics.
To describe the inclination change and the resilient modulus value change an excess pore water pressure conception was utilized. It was found that the M ∆u follows the same pattern but it precedes the M r value change. This is helpful information when performing the stiffness change forecasting.
The pore pressure ratio r u calculated for samples consolidated in an anisotropic manner indicates that the pore pressure ratio had similar characteristics, which in comparison to non-cohesive soils had a higher value in the half of cycle ratio but had a constant rate between the cycle ratio equal to 0.9-1.0 in opposite to non-cohesive soils.
Author Contributions: A.G. conceived and designed the experiments; A.G., E.S. and W.S. performed the experiments; A.G., wrote the paper; W.S. and A.S. edited and audited the content.
Funding: This research received no external funding.

Conflicts of Interest:
The authors declare no conflict of interest.