Open Access

Investigation for the initiation of a loess landslide based on the unsaturated permeability and strength theory

Geoenvironmental Disasters20152:24

DOI: 10.1186/s40677-015-0032-7

Received: 7 October 2014

Accepted: 27 April 2015

Published: 17 September 2015



The Yanlian landslide, occurring on 21-22 October 2010, destroyed many facilities of a big oil refinery in Shaan’xi Province, China. It led to a suspending of the refinery work for a week and caused near 700 million RMB economic losses.


Site exploration shows that the sliding mass is unsaturated-saturated loess. The groundwater is rich in the landslide and shortage in the surrounding slopes. Further investigation finds that the water drop released from the vapor heating furnaces on the top of the slope is the only source of the groundwater. Laboratory tests were performed to get the unsaturated strength parameters and hydraulic conductivity of the loess layers which were applied to a pre-failure slope model to simulate the water infiltration process and the stress field based on which the factor of safety is figured out to analyze the slope stability. Analysis shows that during the first ten years, the factor of safety has no prominent decrease. In the following 5 years, the slope stability decreases significantly till failure.


A little water infiltration has minor effects on slope stability for some time. As a result it is easy to be ignored. However, when the period of water infiltration is long enough to raise the groundwater level, it will have detrimental influence on the stability. In conclusion, any minor water produced by engineering or other activities for a long period may have harmful effect on slope stability. Therefore it is essential to take account of this kind of water and adopt measures to curb the surface water infiltration and to drain the groundwater.


Unsaturated soil Loess Landslide Strength parameters Soil-water characteristic curve Hydraulic conductivity function


Loess landslides occurring in China lead to a huge economic losses every year (Liao et al. 2008; Bai et al. 2012; Li et al. 2012). It has been proved that rainfall, irrigation, water canal leakage, submerging of reservoir, melted snow and earthquake are the main factors triggering loess landslides (Lei, 1994; Dai and Lee 2001; Tu et al. 2009; Li et al. 2013; Zhang & Peng 2014). However, there are no water resources and earthquake mentioned above before the Yanlian landslide occurred, which is located at Luochuan county, Shaanxi province, China as shown in Fig. 1, and the slopes nearby are stable even though they are higher and steeper than the failed. The landslide moves down intermittently for two days and the people working on it has enough time to escape. So there is no fatality in the accident. The cause of the landslide is unclear and deeply concerned by the managers and researchers. The aims of the paper are to find the triggering factors by site exploration and to study the failure mechanism by laboratory tests and numerical analysis.
Fig. 1

Location of the Yanlian landslide

Methods, results and discussions

Characters of the landslides

The landslide occurred on the erosive bank of the Luohe river which is the second tributary of the Yellow river. The first and the third terraces of the river develop on that bank and the second terrace is eroded off. The first terrace, about 5 m above the river bed, is flat and wide on which there is an oil refinery named Yanlian (Fig. 2). Against the rear of the first terrace is a 20 m high rock cliff composed of hard horizontal sandstone of the upper Triassic formation. The rock cliff is the base of the third terrace which is overlain by about 2 m thick alluvial pebble and nearly 50 m thick Quaternary loess successively. The pebble is filled with silt-sand and cemented by leached carbonate calcium, so it has a very low permeability. A spring flows out from the top of the pebble with an average flow quantity of about 0.5 L/s (Fig. 3). The sliding mass, shearing out on the pebble bed, is totally loess. Around the failed slope, there are 34 large oil tanks lying on the top and 24 oil pipelines on the toe. A road wanders on the slope from the toe to the top. A boiler house and a coal storehouse stand on the first terrace against the cliff (Fig. 2).
Fig. 2

The Yanlian landslide
Fig. 3

The spring at the toe of the slope

Several days before October 21, 2010, a small part of loess at the toe of slope started to collapse from where a spring flowed out and buried part of the coal storage house. When the workers were trying to clear the collapsed material, the whole slope moved downwards for two days.

The landslide buried part of the coal storehouse (Fig. 2) and cut off all the 24 oil pipelines (Fig. 4) and the road. The oil tanks were only 5 m away from the head scarp (Fig. 5). The refinery had to stop working until 7 days later when the facilities were recovered. There were no fatalities but it caused 700 million RMB losses.
Fig. 4

The oil transfer pipes cut off by the landslide
Fig. 5

The oil tanks hanging over the top of the head scarp

The surface gradient of the slope before failure is about 30° and the vertical height is 47 m. The failure mass has a width of 240 m, a length of 150 m, a thickness of 13.8 m and a total volume of 400,000 m3. The slope is composed of the unsaturated loess of Late (Q3 loess), Medium (Q2 loess) and Early (Q1 loess) Pleistocene formations as shown in Fig. 6. The groundwater level is only 7 m deep at the center of the landslide, but no groundwater is found in the surrounding slopes. The region is generally shortage of groundwater because of the small precipitation (annually 596 mm/a) and the deep cut landform. The rainfall during the rainy season may quickly run off on the surface. Investigation on the top platform where oil tanks stand finds that there is lots of water vapor released from the pressure adjusters on the heating pipes which are used to keep the oil in the transfer pipes from frozen in winter (Fig. 7). The hot vapor condenses in winter and partly penetrates into the ground. The condensed water of the vapor is possibly the water source in the landslide which has been ignored at the beginning. Therefore it is assumed that the groundwater in the landslide was generated by unsaturated infiltration of the condensed water drops and the landslide was trigged by the rising of the groundwater level.
Fig. 6

The main longitude section of the Yanlian landslide
Fig. 7

The release water vapor from the pressure adjust valves on the heating pipes

Determination of the loess physical properties

The sliding mass and surface are composed of loess. Basic physical properties of loess include permeability, water content, density, plasticity, grain components. The coefficient of saturated permeability was measured through the falling head method. The water content and density were measured by oven drying and metal ring respectively. The plastic limit and liquid limit were measured by hand rolling and Cassgrande apparatus respectively. The results are shown in Table 1. Laser Particle Analysis were utilized to measure the grain size distributions of Q1, Q2, Q3 loess as shown in Fig. 8. It is shown that major component is silt (0.005−0.05 mm) taking up 60 %. The second is clay (<0.005 mm) taking up 20−40 %, and the minor component is fine sand (>0.05 mm) less than 10 %. From Q3 to Q2 and Q1 loess, the mean particle size and the void ratio decrease as well as dry density increases. It demonstrates that the lower the loess layer lies, the longer the time of pedogenesis is and the heavier the load of consolidation experiences, the more compacted the loess is.
Table 1

The basic physical properties of the loess samples



Moisture content

Specific gravity

Dry density

Void ratio

Volumetric moisture content

Liquid limit

Plastic limit

Plastic index

Coefficient of permeability




ρ d/(g/cm3)



w L/(%)

w P/(%)



































Fig. 8

Distribution curves of the particle size for the Q3, Q2, Q1 loess

Determination of SWCC and HCF

Soil-water characteristic curves (SWCC) were measured in laboratory with undisturbed block specimens of 300 mm × 300 mm × 300 mm in dimensions. The specimens were collected from Q1, Q2 and Q3 loess respectively. The matric suctions were measured in wetting processby the TEN−15 tensiometer and the corresponding moisture contents by the oven-drying method. It was accomplished through the following steps: First, a block of specimen was air dried and a hole of 80 mm in depth and 300 mm in diameter was punched in the center of one face of the specimen. Second, insert a tensiometer into the hole with the ceramic head saturated in advance and fill the gap with the same soil powder. Third, the specimen was enclosed with melted wax to make the moister distribution uniform. Some time later, read the data when the matric suction recorded by the gauge is stable. Then remove part of the enclosed wax and collect a bit of soil to measure the water content. So a set of data was obtained. In the next cycle, dropped some water in the specimen and enclosed it again. Repeat the above process to get a new set of data till the suction is 0.

Because the range of tensiometer is less than 100 kPa, the measured data is applied to regress with the Fredlund & Xing’s (1994) eq. (1) to extend the curves to a higher suction range:
$$ {\theta}_w=C\left(\psi \right)\frac{\theta_s}{{\left\{ \ln \left[e+{\left(\psi /a\right)}^n\right]\right\}}^m} $$
Where θ w is the volumetric moisture content; θ s is the saturated volumetric moisture content; ψ is the matric suction; a is the approximate air-entry value of the soil; n is a parameter that controls the slope at the inflection point in the SWCC; m is a parameter related to the residual moisture content; e is the natural number, 2.71828; and C(ψ) is the correcting function defined by eq. (2).
$$ C\left(\psi \right)=1-\frac{ \ln \left(1+\frac{\psi }{C_r}\right)}{ \ln \left(1+{10}^6/{C}_r\right)} $$

Where C r is a constant related to the matric suction corresponding to the residual volumetric moisture content, a typical value for it is 1500 kPa.

The best fitting values of the parameters a, m, n and the regressed SWCC are shown in Fig. 9, in which the dots are the measured values with tensiometer.
Fig. 9

The regressive SWCC curves of the loess, the dots are the measured values with TEN-10 tensiometer

The hydraulic conductivity functions (HCF) is estimated empirically by the model proposed by Childs and Collis-Gorge (1950) and improved by Marshall (1958) and Kunze et al. (1968). The procedure is performed by dividing SWCC into n equal moisture content increments. The relationship between the HCF and the matric suctions is calculated by the model. With the measured saturated coefficients of permeability in Table 1 and the SWCC curves in Fig. 9, the HCF are predicted and shown in Fig. 10.
Fig. 10

The HCF curves of the Q3, Q2, Q1 loess

Measurement of the unsaturated strength parameters c 0 ', φ' and φ b

Fredlund et al. (1978) unsaturated shearing strength is expressed as eq. (3).
$$ {\tau}_f={c}_0^{\prime }+\left(\sigma -{u}_a\right) \tan {\varphi}^{\prime }+\left({u}_a-{u}_w\right) \tan {\varphi}^b $$

Where τ f is the unsaturated shearing strength; c0 is the effective cohesion; φ′ is the effective friction angle; σ-u a is the pure normal strength; u a-u w is the matric suction and φ b is the friction angle related to matric suction.

In which, c0 and φ′ can be measured by conventional direct shear test or triaxial test with saturated specimens. φ b can be measured by suction-controlled direct shear test or triaxial test.

$$ {c}^{\prime }={c}_0^{\prime }+\left({u}_a-{u}_w\right) \tan {\varphi}^b $$
Where, c′ can be considered as the total cohesion which includes the friction produced by matric suction. So, there is
$$ \tan {\varphi}^b=\frac{c^{\prime }-{c}_0^{\prime }}{u_a-{u}_w} $$

Here the total cohesion c′ can be determined against u a-u w by the conventional direct shear test or triaxial test.

For the three layers of Q3, Q2 and Q1 loess as shown in Fig. 6, Q3 lies on the top of the slope and fails due to the tension cracks, so Q3 loess should have lost its strength before the slope failure. Q2 loess fails at a shear zone in the middle of the slope, so consolidated-undrained triaxial tests for Q2 loess were conducted to simulate the stress state. Q1 loess shears outward on the top of the pebble bed horizontally which has a fixed shear direction, so consolidated quick direct tests were conducted on Q1 loess to simulate the confined shear plane.

The moisture content of the loess underground is generally above 5 % while the saturated moisture content is about 30 %. Specimens with initial moisture contents of 5, 10, 15, 20, 25  and 30 % were prepared for Q2 loess and Q1 loess repectively to do the laboratory tests. To make the specimen with intended moisture content, shape and dry each specimen first, then put it on a balance and drop water around it till the total weight is equivalent to the moisture content. After that, the specimens are enclosed in a rubber membrance for a week at least to make the moisture distribution uniform.

Triaxial tests for Q2 loess were performed on the specimens of 80 mm in height and 39 mm in diameter. The confining pressures were set at 100 kPa, 200 kPa, 300 kPa, 400 kPa and 500 kPa rspectively. The rate of axial displacement was set at 0.04 mm/min for all the tests. Direct shear tests for Q1 loess were conducted using the disk specimens of 20 mm in height and 50 mm in diameter. Normal stress was applied with 100 kPa, 200 kPa, 300 kPa, 400 kPa, 500 kPa, 600 kPa and the shear displacement rate was set at 0.02 mm/min.

The triaxial test results are showned in the forms of the maximam shear stress q = (σ 1-σ 2)/2 against axial strain ε 1 and q against average principle stess p = (σ 1 + σ 2)/2 in Fig. 11. It can be seen that the specimens with moisture contents lower than 10 % have no pore watetr presure produced in the whole shearing process, but those with higer moisture contents produce pore water presure. The higher the moisture content, the higher the pore water presure is. Specimens with 5 % moisture contents have remarkable peak values than that of 10 % moisture contents under low confining pressure of 100 kPa. Meanwhile, most of the other specimens have realistic elasto-plastic and hardening stress–strain forms. Some of the high moisture content specimens have gentle softening stress–strain curves, while the strain soften can be attributed to the increase of pore water pressure. It manifests that the loess could maintain the stuctural strength in the condition of low moisture content and low confning pressure. For high moisture content and high confining pressure, the stucture would be broken during consolidation prior to shearing.
Fig. 11

Stress–strain curves and stress paths for the specimens of definite moisture contents (a1)-(a6) are the q-ε 1 curvesand (b1)-(b6) are the stress path q-p curves for the specimens with w = 5, 10, 15, 20, 25, 30 % respectively, wherein q = (σ 1-σ 2)/2, p = (σ 1 + σ 2)/2

With the stress path q-p curves, the effective strength K f lines can be drawn as the common tangent lines of effective stress paths, and the total effective cohesion c' and friction angle φ' can be calculated by intercept b and gradient angles α of K f lines with eq. (5). The obtained unsaturated strength parameters, the moisture contents, the calculated volumetric moisture contents and the matric suction obtained from the SWCC curves are listed in Table 2.
$$ \begin{array}{l}\mathrm{c}\mathit{\hbox{'}}={\mathrm{bcos}}^{-1}{\upvarphi}^{\mathit{\hbox{'}}}\\ {}\upvarphi \mathit{\hbox{'}}={ \sin}^{-1}\left( \tan \upalpha \right)\end{array} $$
Table 2

The measured effective strength parameters and the relevant indexes for Q2 loess



Moisture content

Volumetric moisture content

Matric suction

Total effective cohesion

Effective friction angle


θ w /(%)

U a -u w /(kPa)







































Strength parameters

φ b = 19.5°

c′ 0 = 3.50 kPa

φ′ = 25.0°

Where b is the intercept and α is the gradient of K f line respectively.

The data in Table 2 shows that the effective friction angle φ' is independent of the moisture content. The range of the angles is between 24.5° and 25.5°. The mean value is φ′ = 25.0°. The total effective cohesion c' has a reverse relation with the moisture content. It decreases prominently in the low moisture content range. As the moisture content exceeds the plastic limit (PL = 22.8 %), it reaches to its minimum value 3.50 kPa or so and keeps constant. So c′ 0 is accepted as 3.50 kPa.

The curve of c′-c′ 0 verse u a -u w , shown in Fig. 12, expresses that the relationship of c′-c′ 0 and u a -u w is linear and the gradient angle of the linear curve is 19.5°.
Fig. 12

The relation between c′-c′ 0 against u a -u w of the Q2 loess

The stress–strain curves of the direct shear for Q1 loess are shown in Fig. 13. It can be seen that the marked peak values appear in the cases of low normal stresses and low moisture contents, such as in the moisture contents of 5 % and 10 % under normal stress from 100 kPa to 400 kPa. For the remaining specimens, the stress-strains show realistic elasto-plastic behavior or hardening, similar to the triaxial results of Q2 loess. Assuming 6 mm shear displacement as the failure point, the shear strength against mormal stress for each moisture content are ploted in Fig. 14, from which the total effective cohesions c′ and effective friction angles φ′can be calculated by eq. (5) and are listed in Table 3. The moisture contents, the calculated volumetric moisture contents and the matric suction determined by SWCC curves are also listed in Table 3.
Fig. 13

The shear stress–strain curves of the test results for different moisture contents (a)w = 5 %; (b)w = 10 %; (c)w = 15 %; (d)w = 20 %; (e)w = 25 %; (f)w = 30 %
Fig. 14

The shear strength vs normal stress for different moisture contents

Table 3

The measured effective strength parameters and the relevant indexes for Q1 loess



Moisture content

Volumetric moisture content

Matric suction

Total effective cohesion

Effective friction angle


θ w /(%)

u a -u w /(kPa)







































Strength parameters

φ b = 25.3°

c′ 0 = 5.0 kPa

φ′ = 30.0°

Similar to the triaxial results for Q2 loess, the effective friction angle is independent of the moisture content. The range of the angles is between 29.4° and 30.5°. The mean value is φ′ = 30.0°. The total effective cohesion decreases with the increase of the moisture content and changes prominently in the low range. It reaches to the minimum value of 5.0 kPa or so as the moisture content decreases to plastic limit (PL = 20.8 %). So c′ 0 = 5.0 kPa. Through the curve of c′-c′ 0 verse u a -u w as shown in Fig. 15, φ b can be determined to be 25.3°.
Fig. 15

Relation between c′-c′ 0 and u a -u w of the Q1 loess

Analysis for the landslide initiation mechanism

To analyze the initiation mechanism of the landslide, a 2D FEM model of the slope before failure is built up to simulate the water seepage processes and to monitor the moisture field. The stress field and the strength variation with the moisture change are also analyzed. Fig. 16 shows the FEM model. Geo-studio SEEP and SIGMA software are utilized to simulate the seepage process and the stress fields, respectively.
Fig. 16

FEM meshes of the slope model before failure (Fs = 1.44)

The HCF of Q1, Q2, Q3 loess, the SWCC and the related strength parameters of Q1, Q2 loess have been fully documented above. The strength of Q3 loess can be neglected, so a low cohesion is assigned to it empirically and the friction angle is taken as zero. The deformation parameters of elastic module and Poisson’s ratio have minor effect on the stress field, so values of these parameters for all the strata are assigned empirically. The strength of the bedrock is much higher than the loess strata, so a high cohesion and friction angle are assigned. The values for all the parameters needed in the simulation are summarized in Table 4.
Table 4

The values of the parameters for the slope simulation


Q3 loess

Q2 loess

Q1 loess


Elastic module E/(kPa)





Poisson’s ratio ν





Effective friction angle φ′/(°)





Friction angle related to suction φ b/(°)





Saturated effective cohesion c′ 0/(kPa)





Density γ/(g/cm3)





Saturated permeability K/(m/d)





Initial moisture content w 0/(%)





Initial volumetric moisture content θ 0 /(%)





Initial matric suction (u a -u w \0/(kPa)





The initial condition starts as water begins to drop in the zone of the oil tanks standing on top of the slope. By estimating the voulme of the dropping water into the ground in winter, a 20 mm high and 5 m wide water column is supposed to seep into the ground perday and continue for 100 days (winter days) a year. The rainfall is negleted. In addition, the initial moisture contents of the loess layers are defined by the moister content logging in the borehole in the nearby slope.

Geo-studio SEEP is used to simulate the seepage processes. The moisture field (expressed as pore water pressure field) is added into the Geo-studio SIGMA to simulate the stress and the strength variation under water infiltration. The sliding surface is fixed as the real occurred one, and the shear stress as well as shear strength at each point on the sliding surface can be figured out with the simulated stress states. The factor of safety Fs is defined by eq. (6) based on limit equilibrium theory.
$$ Fs=\frac{{\displaystyle {\int}_{x_A}^{x_B}{\tau}_f}dx}{{\displaystyle {\int}_{x_A}^{x_B}\tau dx}} $$

Where τ f is the shear strength of the sliding surface as defined by eq. (3); τ is the shear stress on the sliding surface; x A and x B are the horizontal coordinate of the end points of the sliding surface.

The simulations are conducted from the beginning of water dropping and the factor of safety is calculated as well till it fails. At last, it keeps stable for 15 years before failure. The period is agreement with the age of the oil tanks.

Figure 17 shows the simulated pore water pressure fields at specified time. For each year, the results at the ends of 100 days water dropping and after 265 days break are provided. It shows that in the first year, the moisture perches at the upper layer of the slope. And when stopping infiltrating, the moisture scatters and negative pore pressure decreases. In the 4th year, moisture moves down to the impermeable rock bed and migrates along the boundary of Q3 and Q2 loess as well as the bedrock. When the infiltration stops, the wetting front moves laterally and the groundwater level decreases with the water extends outwards. However, at this time, just a little moisture invades the sliding surface, so the slope stability has no significant change. In the 9th year, the groundwater rises up to submerge the lower portion of the sliding surface and the slope stability starts to decrease. During the drop break, the groundwater continues flowing from the inner to the slope toe. As a result the groundwater level beneath the slope toe continues rising. So in all the yearly periods, the slope stability becomes worse even after the water stops infiltrating.
Fig. 17

The simulated results of the pore water pressure in the slope at different times (a) At the end of 100 days, Fs = 1.43; (b) At the end of the first year, Fs = 1.43; (c) At the end of the 4th year and 100 days, Fs = 1.44; (d) At the end of the 5th year, Fs = 1.43; (e) At the end of the 9th year and 100 days, Fs = 1.36; (f) At the end of the 9th year, Fs = 1.29; (g) At the end of the 14th year and 100 days, Fs = 1.03; (h) At the end of the 14th year, Fs = 1.01

Figure 18 shows the evolution of the factor of safety during water infiltration. During the first eight years, the factor of safety has no prominent decreasing and begins to lower in the 9th-10th years. The time coincides with the period that the groundwater level begins to touch the potential sliding surface and rises continuously. In addition, the moisture content of the slope above the groundwater level also increases which reduces the strength of the loess. All of these factors lead to the slope failure.
Fig. 18

The factor of safety varied with time


Loess is a typical unsaturated soil which is sensitive to moisture. In this paper, investigation demonstrates that long term condensed water vapor released from the pressure adjusters on the heating pipes which are used to keep the oil in the transfer pipes from frozen in winter is the triggering factor of the Yanlian landslide. Laboratory tests including conventional triaxial tests, consolidation quick shear tests and SWCC measurement are performed to estimate the unsaturated strength parameters and water conductivity.

The safety of factor can be figured out based on the moisture field and the stress field simulated by the FEM model with the parameters. The result shows that a little water infiltration has minor effects on slope stability for some time. As a result it is easy to be ignored. However, when the period of water infiltration is long enough to raise the groundwater level, it will have detrimental influence on the stability and the slope will fail at last. The analysis above illustrates that any minor water produced by engineering or other activities may have harmful effect on slope stability for a long period of action. Therefore it is essential to take account of this kind of water and adopt measures to curb the surface water infiltration and to drain the groundwater.



This research was funded by one of National Basic Research Program of China (2014CB744701) and National Natural Science Foundation of China (Program no. 41372329). The authors wish to acknowledge Dr. Austin ChukwuelokaOkeke, Department of Geoscience, Shimane University, for reading the manuscript and revising the English language. Our thanks also give to Dr. Xianli Xing, Department of Geological Engineering, Chang’an University, for her valuable guidance of the laboratory tests.

Open AccessThis article is distributed under the terms of the Creative Commons Attribution 4.0 International License (, which permits unrestricted use, distribution, and reproduction in any medium, provided you give appropriate credit to the original author(s) and the source, provide a link to the Creative Commons license, and indicate if changes were made.

Authors’ Affiliations

Department of Geological Engineering, Chang’an University


  1. Bai MZ, Du YQ, Kuang X (2012) Warning Method and System in Risk Management for Loess Engineering Slopes. J Perform Constr Facil 26(2):190–196View ArticleGoogle Scholar
  2. Chillds EC, Collis-Geoge GN (1950) The permeability of porous materials. Proc R Soc London, Ser A 201:392–405View ArticleGoogle Scholar
  3. Dai FC, Lee CF (2001) Frequency-volume relation and prediction of rainfall-induced landslides. Eng Geol 59(3/4):253–266View ArticleGoogle Scholar
  4. Fredlund DG, Morgenstern NR, Widger RA (1978) The shear strength of unsaturated soils. Can Geotech J 15:313–321
  5. Fredlund DG, Xing A (1994) Equations for the soil-water characteristic curve. Can Geotech J 31(3):521–532View ArticleGoogle Scholar
  6. Kunze RJ, Uehara G, Graham K (1968) Factors important in the calculation of hydraulic conductivity. Soil Sci Soc Am Proc 32:760–765View ArticleGoogle Scholar
  7. Lei XY (1994) The hazards of loess landslides in the southern tableland of Jingyang County, Shaanxi and their relationship with the channel water into fields (In Chinese). J Eng Geol 3(1):56–64Google Scholar
  8. Li P, Zhang B, Li TL (2012) Study on Regionalization for Characteristic and Destruction Rule of Slope in Loess Plateau (In Chinese). J Earth Sci Environ 34(3):89–98Google Scholar
  9. Li TL, Wang P, Xi Y (2013). Mechanisms for initiation and motion of Chinese loess landslides, Ed. by FawuWang, Masakatsu Miyajima, Tonglu Li,Wei Shan, Teuku Faisal Fathani, Progress of Geo-Disaster Mitigation Technology in Asia, Springer, Verlag Berlin Heidelberg:105-122.
  10. Liao HJ, Su LJ, Li ZD, Pan YB, Fukuoka H (2008) Testing study on the strength and deformation characteristics of soil in loess landslides. Ed. by Chen Zuyu, Zhang Jianmin, Li Zhongkui, Wu Faquan, Ho Ken, Landslides and Engineered Slopes (from the Past to the Future), CRC Press, Leiden, The Netherlands, Vol 1:443-447.
  11. Marshall TJ (1958) A relation between permeability and size distribution of pores. J Soil Sci 9:1–8View ArticleGoogle Scholar
  12. Tu XB, Kwong AKL, Dai FC, Tham LG, Min H (2009) Field monitoring of rainfall infiltration in a loess slope and analysis of failure mechanism of rainfall-induced landslides. J Eng Geol 105(1):134–150View ArticleGoogle Scholar
  13. Zhang JQ, Peng JB (2014) A coupled slope cutting—a prolonged rainfall-induced loess landslide: a 17 October 2011 case study. Bull Eng Geol Environ 73(4):997–1011View ArticleGoogle Scholar


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