Analytical Solution for One-Dimensional Nonlinear Consolidation of Saturated Double-Layered Soil Subjected to Cyclic Loadings

Kim, Pyol; Pak, Chol-U; Myong, Hakbom

doi:https://doi.org/10.1155/2021/5595232

Journal of Engineering

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Abstract Introduction Conclusion Appendix Data Availability Conflicts of Interest References Copyright Related Articles

Research Article | Open Access

Volume 2021 | Article ID 5595232 | https://doi.org/10.1155/2021/5595232

Analytical Solution for One-Dimensional Nonlinear Consolidation of Saturated Double-Layered Soil Subjected to Cyclic Loadings

Pyol Kim,¹Chol-U Pak,¹and Hakbom Myong¹

Academic Editor: Francesco Colangelo

Received11 Feb 2021

Revised17 Aug 2021

Accepted22 Oct 2021

Published09 Nov 2021

Abstract

Cyclic loading-induced consolidation behavior of soft soil is of great interest for the analysis of offshore and onshore structures. In this study, an analytical solution for one-dimensional (1D) nonlinear consolidation of saturated double-layered soil under various types of cyclic loadings such as trapezoidal cyclic loading, rectangular cyclic loading, and triangular cyclic loading was derived. The proposed solution was subsequently degenerated into solutions for special cases and compared to the existing solutions. The degenerate solutions show good agreement with the existing results, which proves that the proposed solutions are more general ones for 1D nonlinear consolidation of saturated soils under time-dependent loading. Finally, a comprehensive parametric study was conducted to investigate the influences of different layer parameters, drainage conditions, and loading parameters on nonlinear consolidation of saturated double-layered soil under cyclic loadings.

1. Introduction

Soft soil beneath most of the marine structures is saturated and can be subjected to various types of cyclic loads. The sources of cyclic load include traffic loads on roads, highways, railways, and airports; silos or tanks filling and discharging; wave and wind actions for offshore structures; and so on. For those structures built on soft soil, predicting the cyclic loading-induced consolidation deformation is a very important design issue.

Up to the present, a number of methods have been proposed for consolidation analysis of saturated soil subjected to cyclic loadings, which can generally be divided into two categories according to the adopted main assumptions. Many scholars have presented different solutions for a consolidation of saturated soil under various cyclic loadings such as rectangular cyclic loading [1], haversine cyclic loading [2–4], and the other types of cyclic loadings [5, 6]. However, those solutions are based on the linear assumption that the compressibility and the permeability of soil are constant during the consolidation process, which is a well-known drawback of the linear consolidation theory. In order to overcome this shortcoming, a number of studies have been performed to consider nonlinear consolidation characteristics of soft soil. Several investigators [7, 8] analysed 1D nonlinear consolidation of soil subjected to rectangular cyclic loading using superimposing rule. In addition, numerous researchers have employed the nonlinear assumption proposed by Davis and Raymond [9] and studied the nonlinear consolidation of soil under different types of cyclic loadings [10–13]. Furthermore, Geng et al. [14], Cai et al. [15], and Kim et al. [16] developed solutions for 1D nonlinear consolidation of saturated soil subjected to cyclic loading by considering the variable consolidation coefficient.

All the research works mentioned above only considered the single-layer soil and did not take the layered characteristics of soil into consideration. In view of this, a number of researchers made great contributions to the consolidation theories of saturated layered soil in recent years [17–24]. Among them, Hu et al. [24] applied the differential quadrature method to analyse cyclic loading-induced nonlinear consolidation behavior of saturated multi-layered soil. However, due to the complexity of the nonlinear consolidation equation, none of the researchers have ever derived any analytical solutions for 1D nonlinear consolidation of soil taking both the layered characteristics of soil and the cyclic loading condition into account.

In this paper, analytical solutions are derived for 1D nonlinear consolidation of saturated double-layered soil under different cyclic loadings such as trapezoidal cyclic loading, rectangular cyclic loading, and triangular cyclic loading. The proposed solutions are degenerated into existing solutions in previous literature. A comprehensive parametric study is conducted to investigate the influences of different layer parameters, drainage conditions, and loading parameters on nonlinear consolidation behavior of saturated double-layered soil under cyclic loadings.

2. Mathematical Model

Figure 1 illustrates the schematic model for 1D nonlinear consolidation of double-layered soil subjected to time-dependent loading, where , and are the thickness, the initial coefficient of permeability, the initial coefficient of compressibility, and the consolidation coefficient of the i-th soil layer (i = 1, 2), respectively. H is the total thickness of soil that satisfies . is the uniformly distributed time-dependent loading applied on the top surface of the soil.

Based on Davis and Raymond’s nonlinear consolidation theory, the governing equation for 1D nonlinear consolidation of double-layered soil subjected to time-dependent loading can be written as follows:where and are the excess pore water pressure and the effective vertical stress in the i-th soil layer, respectively; z is the spatial coordinate as shown in Figure 1; and t is time.

According to the assumption that the decrease in permeability is proportional to the decrease in compressibility during the consolidation process of soil, the consolidation coefficient is given by , in which is the unit weight of water; , where and are the compression index and the initial void ratio in the i-th layer corresponding to the initial effective vertical stress , respectively. By the assumption that the distribution of initial effective stress is constant with depth, .

Using Terzaghi’s principle of effective stress, can be written as follows:

In order to simplify equation (1), a new variable can be defined as follows:

Then, equation (1) can be simplified in terms of as follows:where

The initial condition for equation (4) in terms of and can be given by

The boundary conditions in terms of and can be written as follows:where and .

3. Derivation of Solutions for Cyclic Loadings

3.1. Solutions for Trapezoidal Cyclic Loading

3.1.1. Excess Pore Water Pressure

From equations (2) and (3), the excess pore water pressure for double-layered soil subjected to time-dependent loading can be written as follows:where can be obtained by equations (A.10)–(A.13) according to drainage conditions. The detailed derivation for is shown in Appendix A.

Trapezoidal cyclic loading shown in Figure 2 can be expressed as follows:where is the maximum loading; is the period of one loading cycle; and are the loading parameters corresponding to the rate of loading increment or decrement and the rest period of loading, respectively; and is the cycle number.

By solving the integrals in equations (A.10)–(A.13) for the trapezoidal cyclic loading function, complete solutions for the excess pore water pressure of saturated double-layered soil under trapezoidal cyclic loading can be expressed as follows:where

For a single drainage condition,

For a double drainage condition,where and can be given by equations (A.2), (A.6), (A.14), and (A.15) according to drainage conditions. and can be obtained by equations (A.3) and (A.5), respectively.

The expressions of (i.e., , and ) are as follows:where

3.1.2. Average Degree of Consolidation

The average degree of consolidation can be expressed either by settlement or by effective stress. The average degrees of consolidation for double-layered soil subjected to time-dependent loading can be written as follows [22]:where , , , and are average degrees of consolidation in terms of settlement and effective stress for each layer, respectively, defined as follows:

For trapezoidal cyclic loading, complete solutions for the average degrees of consolidation can be written as follows:where for a single drainage condition and for a double drainage condition.

3.2. Solutions for Rectangular and Triangular Cyclic Loadings

Trapezoidal cyclic loading can be degenerated into rectangular cyclic loading and triangular cyclic loading. When , trapezoidal cyclic loading reduces into rectangular cyclic loading (Figure 3(a)). On the other hand, trapezoidal cyclic loading reduces to triangular cyclic loading (Figure 3(b)) when .

(a)

(b)

Analytical solutions for the excess pore water pressure under rectangular cyclic loading and triangular cyclic loading can be obtained substituting and into equation (12), respectively. Similarly, the average degrees of consolidation in terms of settlement and effective stress can also be given by equations (17) and (18).

4. Degeneration to Special Cases

The proposed solutions can be degenerated into existing solutions for 1D nonlinear consolidation of saturated double-layered soil under constant and ramp loadings and saturated single-layer soil under trapezoidal cyclic loading.

4.1. Solutions for Double-Layered Soil under Constant Loading

When , and , trapezoidal cyclic loading reduces to constant loading (Figure 4(a)) expressed by . Then, the solution can be obtained as follows:where can be written as follows.

(a)

(b)

For a single drainage condition,

For a double drainage condition,

Equations (19)–(21) are the solutions for double-layered soil subjected to constant loading proposed by Xie et al. [22].

4.2. Solutions for Double-Layered Soil under Ramp Loading

When and tend to infinity, trapezoidal cyclic loading reduces to ramp loading (Figure 4(b)) given bywhere .

The solutions for double-layered soil under ramp loading can be obtained bywhere can be written as follows:

For a single drainage condition,

For a double drainage condition,

Equations (24)–(26) are the solutions for double-layered soil under ramp loading proposed by Xie et al. [22].

4.3. Solutions for Single-Layer Soil under Trapezoidal Cyclic Loading

When , the solutions for double-layered soil reduce to the solutions for single-layer soil. Therefore, the proposed solutions can be reduced to the solutions for 1D nonlinear consolidation of saturated single-layer soil subjected to trapezoidal cyclic loading as follows:where

(for single drainage condition) and (for a double drainage condition).

Equations (28)–(30) are the solutions for 1D nonlinear consolidation of single-layer soil under trapezoidal cyclic loading presented by Xie et al. [10].

Figure 5 shows the comparison between the degenerate solutions and the existing solutions for double-layered soil subjected to constant loading (Figures 5(a) and 5(b)) and ramp loading (Figure 5(c)) and single-layer soil subjected to trapezoidal cyclic loading (Figure 5(d)). It can be found that the degenerate solutions from this paper show good agreement with the existing results, which proves that the proposed solutions are more general ones for 1D nonlinear consolidation of saturated soils under time-dependent loading.

(a)

(b)

(c)

(d)

5. Parametric Study

In this section, a comprehensive parametric study is conducted to investigate the influences of different layer parameters, drainage conditions, and loading parameters on nonlinear consolidation behavior of saturated double-layered soil under various cyclic loadings.

5.1. Influence of Layer Parameters

In order to investigate the influences of layer parameters such as the permeability ratio K (i.e., ), the compressibility ratio b (i.e. ), and the thickness ratio c (i.e., ), the saturated double-layered soil of total thickness H = 10 m with single drainage condition under various cyclic loadings is considered. The cyclic loadings are trapezoidal () and rectangular and triangular cyclic loadings with , and , where is time factor defined by .

5.1.1. The Permeability Ratio K

For the effect of K, it is assumed that b = 1 and c = 1. Figure 6 presents the excess pore pressure isochrones at the end of loading and unloading stages of the 10th cycle for trapezoidal cyclic loading. Cyclic loadings include loading stage and unloading stage in each cycle unlike static loading, which results in squeezing out of pore water during loading stage and then absorbing during unloading stage. Thus, the excess pore pressures have both positive values for the loading stage and negative values for the unloading stage as shown in Figure 6. It can be shown that the excess pore pressure is smaller for the bigger value of K in the lower layer, while K has no significant effects in the upper layer. It implies that the bigger permeability of the lower layer leads to the faster dissipation rate of pore pressure when the compressibilities of the two layers are the same.

Figure 7 shows the variations of average degrees of consolidation in terms of settlement and effective stress with time factor under different values of K for trapezoidal cyclic loading (Figure 7(a)), rectangular cyclic loading (Figure 7(b)), and triangular cyclic loading (Figure 7(c)). The time factor is defined by . It can be seen that there are almost no differences in U_s and U_p between different values of K at the early stages of consolidation, but the greater K increases the rates of settlement and dissipation of excess pore pressure with fluctuation as time grows. Moreover, the effects are obvious for the case of K < 1 but not clear for the opposite case. It can be explained that the effects of K is mainly related to the permeability of the lower layer, indicating that for a single drainage condition, the smaller permeability of the lower layer decreases the rates of settlement and dissipation of excess pore pressure.

(a)

(b)

(c)

5.1.2. The Compressibility Ratio b

The effect of the compressibility ratio b is investigated for double-layered soil with K = 1 and c = 1. Figure 8 illustrates the excess pore pressure isochrones at the end of loading and unloading stages of the 10th cycle for trapezoidal cyclic loading. It can be found that when the permeabilities of the two layers are the same, the greater the compressibility ratio b is, the greater the excess pore pressure is, indicating that an increase in the compressibility of the lower layer will decrease the rate of consolidation.

The effect of the compressibility ratio b can also be found in Figure 9. Figure 9 represents the variations of average degree of consolidation in terms of effective stress U_p with time factor under different values of b for three different cyclic loadings, such as trapezoidal cyclic loading (Figure 9(a)), rectangular cyclic loading (Figure 9(b)), and triangular cyclic loading (Figure 9(c)). Similar to the above-mentioned result, it can be seen that the increase in the compressibility ratio b decreases the dissipation rate of excess pore pressure with fluctuation when the permeabilities of the two layers are the same.

(a)

(b)

(c)

5.1.3. The Thickness Ratio c

The effect of the thickness ratio c is studied for two cases of double-layered soil: Case 1 is for K = 2 and b = 1 and Case 2 is for K = 1 and b = 2. Figure 10 depicts the excess pore pressure isochrones at the end of loading and unloading stages of the 10th cycle for trapezoidal cyclic loading. It can be found that excess pore pressure decreases when the thickness ratio c increases for Case 1, but the opposite occurs for Case 2. It implies that in the lower layer with higher permeability, the greater thickness results in the smaller excess pore pressure, whereas the increase in thickness of the lower layer with higher compressibility leads to the bigger excess pore pressure.

(a)

(b)

Figure 11 demonstrates the variations of average degree of consolidation in terms of settlement U_s with time factor under different values of the thickness ratio c for trapezoidal cyclic loading (Figures 11(a) and 11(b)), rectangular cyclic loading (Figures 11(c) and 11(d)), and triangular cyclic loading (Figures 11(e) and 11(f)). It can be seen that the effect of the thickness ratio c is similar to the above described in Figure 10. For Case 1, the rate of settlement increases a little with fluctuation when the thickness ratio c increases. As for Case 2, the effect of the thickness ratio c is opposite. In addition, the rate of settlement increases obviously when the thickness of the lower layer with higher compressibility decreases.

(a)

(b)

(c)

(d)

(e)

(f)

5.2. Influence of Drainage Conditions

The influence of drainage conditions is investigated for double-layered soil with K = 2, b = 1, and c = 1. Figure 12 shows the variations of average degrees of consolidation in terms of settlement and effective stress with time factor under different drainage conditions for trapezoidal cyclic loading (Figure 12(a)), rectangular cyclic loading (Figure 12(b)), and triangular cyclic loading (Figure 12(c)). It can be found that the rates of settlement and dissipation of excess pore pressure for a double drainage condition are bigger than those for a single drainage condition. Moreover, the amplitudes of fluctuation in the rates of settlement and dissipation of excess pore pressure under a double drainage condition are also greater than those under a single drainage condition.

(a)

(b)

(c)

5.3. Influence of Loading Parameters

The influence of loading parameters such as , and is analysed for double-layered soil with K = 2, b = 2, and c = 1.

5.3.1. The Loading Parameter

Figure 13 presents the variations of average degrees of consolidation U_s and U_p with time factor under cyclic loadings with different values of . It can be seen that both the settlement rate and the dissipation rate of excess pore pressure decrease with the increase of the value of . The loading parameter reflects the rate of increment or decrement of loading, and thus, it can be concluded that the greater the rate of increment or decrement of loading, the greater the rate of consolidation. In this context, the rate of consolidation for rectangular cyclic loading is the biggest and the rate of consolidation for triangular cyclic loading is the smallest.

5.3.2. The Loading Parameter

Figure 14 depicts the variations of average degrees of consolidation U_s and U_p with time factor under trapezoidal cyclic loading (Figure 14(a)), rectangular cyclic loading (Figure 14(b)), and triangular cyclic loading (Figure 14(c)) with different values of . It can be found that the increase of the value of results in the smaller rates of settlement and dissipation of excess pore pressure and less cycles and bigger amplitude of fluctuation in the rates of settlement and dissipation of excess pore pressure. The loading parameter reflects the rest period of cyclic loadings. Therefore, it can be concluded that the rate of consolidation under cyclic loadings increases with the decrease of the rest period of cyclic loading. As a result, the rate of consolidation under cyclic loadings without rest period (i.e., ) is the biggest; especially, the rectangular cyclic loading without rest period reduces the constant loading, and the rate of consolidation under constant loading is the highest.

(a)

(b)

(c)

5.3.3. The Loading Parameter

Figure 15 represents the variations of average degrees of consolidation U_s and U_p with time factor under trapezoidal cyclic loading (Figure 15(a)), rectangular cyclic loading (Figure 15(b)), and triangular cyclic loading (Figure 15(c)) with different values of . It can be seen that a smaller value of induces more cycles and smaller amplitude of fluctuation in the rates of settlement and dissipation of excess pore pressure, but the loading parameter has no effects on the average values of the rates of settlement and dissipation of excess pore pressure. Since the loading parameter reflects the period of loading, it can be found that the longer the period of loading, the bigger amplitude and less cycles of fluctuation in the settlement rate and the dissipation rate of excess pore pressure.

(a)

(b)

(c)

6. Conclusion

In this paper, analytical solutions have been presented for 1D nonlinear consolidation of saturated double-layered soil subjected to cyclic loadings such as trapezoidal cyclic loading, rectangular cyclic loading, and triangular cyclic loading. It shows through the degeneration of the proposed solutions into special cases that the solutions presented in this paper are more general for the nonlinear consolidation of saturated soils under time-dependent loading. Based on the proposed solutions, a comprehensive parametric study is conducted, and the following conclusions can be drawn:(1)The nonlinear consolidation of saturated double-layered soil under cyclic loadings is affected by layer parameters such as the permeability ratio, the compressibility ratio, and the thickness ratio. The smaller permeability of the lower layer decreases the rates of settlement and dissipation of excess pore pressure. An increase in the compressibility of the lower layer will decrease the rate of consolidation. Furthermore, the rate of settlement increases when the thickness of the lower layer with higher compressibility decreases.(2)The drainage conditions have great effects on the nonlinear consolidation behavior of saturated double-layered soil under cyclic loadings. The rates of settlement and dissipation of excess pore pressure and the amplitudes of fluctuation in the rates for a double drainage condition are bigger than those for a single drainage condition.(3)The loading parameters have significant influences on the nonlinear consolidation behavior of saturated double-layered soil subjected to various cyclic loadings. The greater the rate of increment or decrement of loading, the greater the rate of consolidation. The rate of consolidation under cyclic loadings increases with the decrease of the rest period of cyclic loadings. The longer the period of loading, the bigger amplitude and less cycles of fluctuation in the settlement rate and the dissipation rate of excess pore pressure.

Appendix

A. The Derivation of General Solutions for

The general solutions of equation (4) for a single drainage condition can be assumed as follows:where ; , and are unknown coefficients to be found; and is a function of , resulting from .

Substituting equation (10) into the boundary condition equation (8), we can get as follows:where

Substituting equation (10) into (4) and simplifying, and can be obtained as follows:

In order to determine , the eigen equation can be obtained by substituting equation (10) into the boundary condition equation (9) as follows:

Furthermore, using the coefficients obtained above, we can get the following relations:

Using the following orthogonal relation,

and can be written as follows:

Now, substituting all those coefficients into equation (10), the general solutions of equation (4) for a single drainage condition can be written as follows:

Similarly, the general solutions of equation (4) for a double drainage condition can be obtained as follows:where

The eigen equation for can be obtained as follows:

Data Availability

The data used to support the findings of this study are included within the article.

Conflicts of Interest

The authors declare that there are no conflicts of interest.

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Copyright © 2021 Pyol Kim et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

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