Simplified Liquefaction Prediction and Assessment Method Considering Waveforms and Durations of Earthquakes
Publication: Journal of Geotechnical and Geoenvironmental Engineering
Volume 143, Issue 2
Abstract
This paper presents a new simplified liquefaction prediction and assessment method that is capable of considering the influence of the waveforms and durations of earthquakes. The concept of an effective number of waves was introduced to represent the characteristics of the irregularity of waveforms and the different number of load cycles of irregular seismic motions, as well as their influence on the occurrence of liquefaction. A comprehensive set of laboratory liquefaction tests and statistical analyses were performed to study and validate this concept. The validity of the proposed method, which adopts a wave correction coefficient based on the proposed concept, was verified using the case histories of five past major earthquakes, demonstrating that the predictive capability of the new method was improved compared with that of the conventional method for the cases of liquefaction and no liquefaction. A unique feature of the new simplified method is its universality, allowing it to be applied to various types of liquefaction charts, facilitating more-rational liquefaction prediction and assessment worldwide.
Introduction
Liquefaction prediction and assessment is a vital part of the earthquake-resistant design of structures on liquefiable soils. Liquefaction prediction and assessment charts, originally developed by Seed and Idriss (1971), have been widely used for such design in practice, as well as for disaster prevention and mitigation. The liquefaction charts are characterized by the relationships between the severity or level of earthquake loading, represented by the cyclic stress ratio, versus the soil liquefaction resistance, represented by field measured values such as the SPT (standard penetration test) -values, i.e., blow counts (Seed et al. 1983, 1985; Tokimatsu and Yoshimi 1983; Iai et al. 1989; Youd et al. 2001; Cetin et al. 2004; Boulanger et al. 2012), CPT (cone penetration test) -values, i.e., tip resistances (Robertson and Wride 1998; Moss et al. 2006; Robertson 2015; Boulanger and Idriss 2015), and shear-wave velocities (Andrus and Stokoe 2000; Andrus et al. 2004; Kayen et al. 2013). These charts have been calibrated against cases in which liquefaction occurred or did not occur at given sites.
Earthquake motions at given sites generally have different waveforms and durations that vary considerably in space and time depending on the characteristics of the sites, routes along which seismic waves propagate, and source rupture process of earthquakes (e.g., Aki and Richards 2009). However, current engineering designs do not adequately consider such earthquake loading characteristics in light of liquefaction, that is to say, the influence of variable waveforms and their durations for given earthquakes, in contrast to soil resistance characteristics, which have been extensively studied and developed, including the aging effect with fines (e.g., Kokusho et al. 2012; Dobry et al. 2015). Indeed, under given maximum ground surface accelerations and maximum cyclic stress ratios at given depths, the results of the corresponding liquefaction prediction and assessment would be the same, for the given soil characteristics, even if there were considerable differences in the waveforms and durations of the seismic motions concerned.
In this study, a new simplified liquefaction prediction and assessment method that is capable of considering the influence of the waveforms and durations of earthquakes is developed. The concept of the effective number of waves is introduced and validated using the results of a comprehensive set of laboratory tests and the case histories of five major earthquakes, including the 2011 Off the Pacific Coast of Tohoku Earthquake. A unique feature of the proposed method is its universality, allowing it to be applied to all types of liquefaction charts mentioned above.
Review of Technical Standards of Liquefaction Charts
This section concisely reviews the essential features of technical standards of liquefaction charts and simplified procedures for liquefaction prediction and assessment. Liquefaction charts commonly represent the relationship between the severity of seismic loading, defined in terms of the cyclic stress ratio versus the field measured resistance represented by the SPT -values (Seed et al. 1983, 1985; Tokimatsu and Yoshimi 1983; Iai et al. 1989; Youd et al. 2001; Cetin et al. 2004), CPT -values (Robertson and Wride 1998; Moss et al. 2006), or shear-wave velocities (Vs) (Andrus and Stokoe 2000; Andrus et al. 2004). Recent developments include reexamination of an updated case history database (Boulanger et al. 2012), use of a probabilistic approach (Kayen et al. 2013), and intermethod comparison of the SPT, CPT, and Vs charts (Robertson 2015; Boulanger and Idriss 2015). All of these charts share the same basic principle and important characteristics.
As an illustrative example, a liquefaction chart based on standard penetration tests (Youd et al. 2001; modified from Seed et al. 1985) is shown in Fig. 1. Here, the -value, , denotes the SPT blow count that is normalized to an overburden pressure of approximately 100 kPa and a hammer energy ratio, or hammer efficiency, of 60%. For liquefaction prediction, one plots the cyclic stress ratio and the -value on this graph; if the plot lies above the given line corresponding to a certain fines content, liquefaction is predicted to occur, otherwise no liquefaction is predicted. Here, the cyclic stress ratio (CSR) is calculated from the following equation:where (Gal) = maximum horizontal acceleration at the ground surface; (kPa) = maximum cyclic shear stress exerted on the soil at a given depth; and (kPa) = initial vertical total stress and initial vertical effective stress, respectively; = gravitational acceleration (980 Gal); and = stress reduction coefficient, with at the ground surface and, typically, below the ground surface. As is evident in Eq. (1), it is based on the assumption that , along with the maximum acceleration estimated at the ground surface. Eq. (1) also offers an alternative approach (Dobry and Abdoun 2011), where the cyclic stress ratio (CSR) is obtained directly from the maximum shear stress calculated with a site response analysis program such as SHAKE (Schnabel et al. 1972).
(1)
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The liquefaction chart in Fig. 1 is for an earthquake magnitude of 7.5. For other magnitudes, magnitude scaling factors are introduced to correct the cyclic stress ratio, based on the assumption that there exist an equivalent number of cycles for a given earthquake (e.g., Youd et al. 2001; Liu et al. 2001). Related aspects of earthquake behavior will be discussed later in this paper.
For the purpose of comparison and subsequent discussion, the liquefaction chart taken from Japanese guidelines (MLIT 2007) is shown in Fig. 2. Here, the equivalent acceleration is defined in terms of the cyclic stress ratio asand the equivalent -value is defined aswhere (Gal) = equivalent acceleration, which is obtained through site response analysis, generally using the code SHAKE (Schnabel et al. 1972); and = equivalent -value corresponding to a vertical effective stress of , where the -value at a given soil depth is obtained from a standard penetration test (SPT). The equivalent -value is adjusted for soils with certain fines contents and plasticity indexes (MLIT 2007).
(2)
(3)
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The occurrence and possibility of liquefaction are predicted and assessed depending on where a given plot point, based on Eqs. (2) and (3), lies in the four zones of the chart. Namely, Zone I means that liquefaction will occur, Zone II represents a high possibility of liquefaction, Zone III represents a low possibility of liquefaction, and Zone IV means that liquefaction will not occur. For a more-accurate evaluation of liquefaction in Zones II and III, one may conduct liquefaction tests in the laboratory using undisturbed soil samples, and together with the results of these tests, one can assess the occurrence or absence of liquefaction. Before applying the aforementioned liquefaction chart, first, screening is performed with soil classification, as shown in Fig. 3. That is to say, there are different ranges of grain-size distributions with a possibility of liquefaction, depending on the grading of the soils. If the soil has a grain-size distribution that falls in the ranges with the possibility of liquefaction, it is assessed that liquefaction can occur, and if not, it is assessed that liquefaction does not occur. In the former cases, the liquefaction chart is used for liquefaction prediction and assessment.
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Converting the horizontal and vertical axes in Fig. 2 and using the line between Zone II and Zone III as a dividing line between liquefaction and no liquefaction, the structure of this chart becomes essentially the same as the chart shown in Fig. 1, where the clean-sand base curve is considered. Indeed, through appropriate conversions (Iai et al. 1989), the Japanese liquefaction chart was previously shown to compare favorably with those of Seed et al. (1985) and Tokimatsu and Yoshimi (1983).
There are some basic assumptions underlying the liquefaction charts with respect to the influence of the waveforms and durations of earthquakes. Those assumptions are such that the nonuniform cyclic shear stress variation exerted on a soil layer during an earthquake can be replaced by an equivalent number of cycles of uniform stress, and there are an equivalent number of loading cycles relating to earthquake magnitudes (Seed et al. 1983; Youd et al. 2001; Liu et al. 2001; Idriss and Boulanger 2008; Dobry and Abdoun 2011). However, these assumptions neither represent nor account for actual field conditions, such as the waveforms and durations of seismic motions varying considerably in space and time due to the characteristics of the sites, routes, and sources of earthquakes (e.g., Aki and Richards 2009).
In what follows, the authors present a new method that incorporates the influence of such waveforms and durations of the earthquakes and that can be applied to any type of the liquefaction charts described earlier.
New Method Considering the Influence of Waveforms and Durations of Earthquakes
A new liquefaction prediction and assessment method that takes account of the influence of waveforms and durations of seismic motions is presented herein. For this purpose, the results of a comprehensive set of laboratory tests will be described first. The concept of the effective number of waves is then discussed and is incorporated into liquefaction prediction and assessment.
Undrained Cyclic Torsional Shear Tests and Constant-Volume Cyclic Simple Shear Tests
Three series of laboratory liquefaction tests were conducted using 11 types of irregular waves with different waveforms and load cycles, as shown in Fig. 4, together with regular waves, comprising a total of 241 test cases. The laboratory tests performed were undrained cyclic hollow cylindrical torsional shear tests for Series 1 and 2 and constant-volume cyclic simple shear tests for Series 3, as listed in Table 1. All of the tests were carried out using reconstituted specimens of silica sand with a median grain size and a uniformity coefficient . The sizes of the hollow cylindrical specimens were 30 mm in internal diameter, 70 mm in external diameter, and 70 mm in height for Series 1, and 60 mm in internal diameter, 100 mm in external diameter, and 100 mm in height for Series 2. The size of the cylindrical specimen, which was confined in 10 circular Teflon polytetrafluorethylene rings each with a thickness of 4 mm, was 100 mm in diameter and 40 mm in height for Series 3. The samples were prepared through air pluviation by adjusting the fall height to achieve the targeted relative densities, and were frozen and set in the cell with subsequent thawing in Series 1, whereas in Series 2 samples were prepared by dry vibratory compaction. In both series, the samples were saturated so that the pore pressure coefficient B became higher than 0.95 and were isotropically consolidated to an effective stress of , and then subjected to undrained cyclic torsional shear with given seismic waves. Series 3 samples were prepared by dry vibratory compaction and were consolidated to a vertical effective stress of , and were then subjected to constant-volume cyclic simple shear with given seismic waves. The 11 types of irregular waves shown in Fig. 4, which had a wide variety of waveforms and durations with the number of seismic waves ranging from 10 to over 300, were collected and/or artificially created on the basis of the seismic records of past earthquakes. The time axes of the loaded seismic waves were calibrated and elongated so as to assure accurate control of the loads during the undrained or constant-volume cyclic shear of the samples (Yamazaki and Emoto 2010).
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Series | Testing method | Sample preparation | (%) | Waveform | ||||
---|---|---|---|---|---|---|---|---|
T-1 | Cyclic torsional shear | Air pluviation | 50 | 0.121, 0.153, 0.200, 0.296 | 0.163 | 1 | 0.229, 0.242, 0.261, 0.276 | 0.247 |
2 | 0.241, 0.253, 0.288, 0.378 | 0.290 | ||||||
3 | 0.203, 0.207, 0.227, 0.251 | 0.221 | ||||||
4 | 0.178, 0.179, 0.188, 0.189 | 0.186 | ||||||
65 | 0.159, 0.178, 0.202, 0.229 | 0.186 | 1 | 0.286, 0.313, 0.351, 0.402 | 0.327 | |||
2 | 0.261, 0.301, 0.398, 0.482 | 0.396 | ||||||
3 | 0.220, 0.235, 0.270, 0.280 | 0.267 | ||||||
4 | 0.227, 0.235, 0.259, 0.273 | 0.246 | ||||||
80 | 0.182, 0.201, 0.301, 0.480 | 0.220 | 1 | 0.352, 0.452, 0.609, 1.031 | 0.422 | |||
2 | 0.345, 0.561, 0.765, 1.060 | 0.514 | ||||||
3 | 0.340, 0.436, 0.513, 0.588 | 0.371 | ||||||
4 | 0.243, 0.264, 0.280, 0.311 | 0.263 | ||||||
5 | 0.261, 0.287, 0.325 | 0.294 | ||||||
90 | 0.214, 0.250, 0.281, 0.330 | 0.260 | 1 | 0.403, 0.615, 0.826, 1.239 | 0.768 | |||
2 | 0.399, 0.628, 0.842, 1.187 | 0.902 | ||||||
3 | 0.412, 0.518, 0.679, 0.910 | 0.613 | ||||||
4 | 0.349, 0.400, 0.443, 0.588 | 0.417 | ||||||
T-2 | Cyclic torsional shear | Vibratory compaction | 50 | 0.172, 0.205, 0.244 | 0.178 | 6 | 0.203, 0.262, 0.306 | 0.271 |
7 | 0.200, 0.259, 0.282, 0.309 | 0.270 | ||||||
8 | 0.213, 0.229, 0.260 | 0.235 | ||||||
9 | 0.208, 0.256, 0.258 | 0.257 | ||||||
10 | 0.204, 0.248, 0.290 | 0.258 | ||||||
65 | 0.182, 0.266, 0.365, 0.480 | 0.242 | 6 | 0.303, 0.402, 0.443 | 0.412 | |||
7 | 0.308, 0.354, 0.410 | 0.365 | ||||||
8 | 0.224, 0.281, 0.314 | 0.288 | ||||||
9 | 0.259, 0.297, 0.301 | 0.284 | ||||||
10 | 0.249, 0.317, 0.360 | 0.327 | ||||||
80 | 0.299, 0.404, 0.506 | 0.348 | 6 | 0.575, 0.617, 0.671 | 2.320 | |||
7 | 0.404, 0.513, 0.622 | 0.540 | ||||||
8 | 0.259, 0.303, 0.410 | 0.318 | ||||||
9 | 0.407, 0.421, 0.449 | 0.421 | ||||||
10 | 0.343, 0.402, 0.453 | 0.404 | ||||||
S | Cyclic simple shear | Vibratory compaction | 40 | 0.085, 0.107, 0.140 | 0.117 | 6 | 0.160, 0.173, 0.183, 0.192 | 0.172 |
7 | 0.149, 0.154, 0.160, 0.161, 0.165 | 0.158 | ||||||
8 | 0.128, 0.142, 0.143, 0.145, 0.147 | 0.144 | ||||||
50 | 0.105, 0.131, 0.144 | 0.123 | 6 | 0.186, 0.191, 0.194, 0.197 | 0.191 | |||
7 | 0.172, 0.174, 0.178, 0.246, 0.293 | 0.175 | ||||||
8 | 0.145, 0.153, 0.155 | 0.146 | ||||||
9 | 0.161, 0.170 | 0.169 | ||||||
10 | 0.172, 0.173 | 0.173 | ||||||
65 | 0.111, 0.158, 0.179 | 0.155 | 6 | 0.238, 0.267, 0.314, 0.356 | 0.286 | |||
7 | 0.170, 0.213, 0.235, 0.254 | 0.215 | ||||||
8 | 0.183, 0.187, 0.188, 0.189 | 0.187 | ||||||
9 | 0.192, 0.202, 0.224, 0.232 | 0.202 | ||||||
10 | 0.171, 0.201, 0.203, 0.210, 0.214 | 0.209 | ||||||
11 | 0.247, 0.318, 0.384, 0.457 | 0.279 | ||||||
80 | 0.130, 0.156, 0.209 | 0.176 | 6 | 0.247, 0.410, 0.573, 0.750 | 0.317 | |||
7 | 0.246, 0.289, 0.337 | 0.264 | ||||||
8 | 0.207, 0.235 | 0.212 | ||||||
9 | 0.201, 0.220, 0.247 | 0.207 | ||||||
10 | 0.180, 0.266, 0.310 | 0.216 | ||||||
90 | 0.176, 0.235, 0.300, 0.360 | 0.283 | 6 | 0.315, 0.803, 1.150, 1.648 | 0.909 | |||
7 | 0.224, 0.296, 0.373, 0.455, 0.602, 0.686 | 0.557 | ||||||
8 | 0.194, 0.252, 0.317, 0.384, 0.515, 0.584 | 0.434 |
The example test results are shown in Fig. 5. It is seen that, with seismic loading, the excess pore-water pressure built up, and shear strain developed. The definition of liquefaction used for all test cases under the regular and irregular wave loading is such that liquefaction takes place when the double-amplitude shear strains reach (Tatsuoka et al. 1986). Indeed, the excess pore pressure reached the level of the effective confining pressure () at around in this case.
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The cyclic shear stress ratio, , versus the number of load cycles, leading to liquefaction for the regular wave loading is shown in Fig. 6. The liquefaction resistance for the regular waves was defined by the cyclic stress ratio with , designated as . For the irregular wave loading, the maximum cyclic stress ratios, , were varied, and their relationships with the developed double-amplitude shear strains, , were plotted, as shown in Fig. 7. The liquefaction resistance for the irregular waves was defined by the maximum cyclic stress ratio corresponding to , designated as . The liquefaction resistances, i.e., cyclic resistance ratios and , obtained for all regular and irregular wave loading cases, are summarized in Table 1, with the relative densities, , ranging from 40 to 90%.
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Effective Number of Waves
The concept of effective number of waves introduced to characterize the waveforms and durations or number of load cycles of irregular seismic waves is described here. The theme here is how to represent the severity of given seismic waves, with certain maximum amplitudes, yet having distinctly variable waveforms and durations. The key idea is that small waves relative to the maximum waves may not make a significant contribution to the occurrence of liquefaction due to the lesser cyclic plasticity of the soils (e.g., Sassa and Sekiguchi 2001). In other words, seismic waves having intensities above certain proportions of the maximum waves may effectively contribute to the occurrence of liquefaction. The proportion of such waves was defined as , and the relationships between , specifically the number of half-waves having intensities above , and the liquefaction susceptibility defined by the ratio was studied. Example relationships are plotted in Fig. 8 for , 20, 30, 40, 50, 60, 70, 80, and 90% and . The dotted lines represent power-function regression curves whose correlations were analyzed for all of the test cases in Table 1. The results of this statistical analysis are shown in Fig. 9. The correlation coefficient, , was lower for low values of . The -value increased with increasing , reached a peak and then decreased with increasing . For , however, the -value was consistently high, which stemmed from the smaller number of test cases for very soft soils, as given in Table 1. Overall, the results indicate that there exists an optimal value of at around . This means that the number of half-waves having intensities above had the highest correlations with . Hence, with reference to Fig. 10, the effective number of waves, , was defined as half the number of half-waves above in the time history of the shear stress variation due to irregular seismic waves, as shown in Fig. 10. By definition, the value becomes equal to in the case of regular seismic waves.
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Ishihara and Yasuda (1973, 1975) classified the waveforms of irregular seismic waves as a shock type and vibratory type, depending on the number of waves preceding the maximum whose amplitudes are greater than 60% of the maximum shear stress . This classification, however, has proven insufficient in characterizing the degree of the irregularity because it was based solely on information regarding the preceding seismic waves before manifested in a given shear stress variation.
A notable feature of the effective number of waves defined above is that it varies not only by the durations or load cycles of the seismic motions, but also by the degree of irregularity of the seismic waveforms through the shear stress variation, such as impulsive or oscillatory waveforms, even for the same durations. As a consequence, the effective number of waves, together with the conventional maximum shear stress, is capable of representing the severity of given seismic loading, simultaneously taking account of the influence of such waveforms and durations of the irregular seismic motions in a simple yet workable way.
The liquefaction resistance for the irregular seismic waves, , is plotted against the effective number of waves, , as shown in Fig. 11. The solid lines represent the power regression curves and the dotted lines will be explained later with reference to the proposed equations. It is seen that the value decreases with increasing , and its dependency varies considerably with .
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Liquefaction Prediction and Assessment
For liquefaction prediction and assessment utilizing the effective number of waves concept, and its wider applications, this subsection considers the normalized liquefaction resistance in terms of the liquefaction resistance for a reference value of , namely , and defines the term as a wave correction coefficient :
(4)
Eq. (4) indicates that under the conditions , then ensues. The index links and through a power function and depends on . Regression analysis of the observed data led to the following form:
(5)
Here, Eq. (5) is valid for , thus, , that is, nearly 30%, and under very soft soil conditions with , it follows that and . Eqs. (4) and (5) indicate that increases for and decreases for . The value can be assessed from the widely used correlation with the SPT -value (Meyerhof 1957; Ishihara 1996):
(6)
Other widely used correlations between and the CPT -value, or between and and (Jamiolkowski et al. 1985; Robertson 1990; Ishihara 1996; Andrus and Stokoe 2000; Andrus et al. 2004, among others) can also be employed for calculating .
With reference to Fig. 11, the dotted lines represent the values predicted from Eqs. (4) and (5). Here, the condition was used, and the corresponding values were adopted from the measured ones (solid lines) in Fig. 11. There are reasonably good agreements between the two. The form of the proposed Eqs. (4) and (5) is kept constant for any value of , which facilitates universal application of the wave correction coefficient, .
The wave correction coefficients, , on the basis of Eqs. (4)–(6) are plotted against and in Fig. 12. It is seen that the value changes more markedly with increasing and . The corresponding procedure for the liquefaction prediction and assessment is described subsequently.
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Liquefaction charts have been constructed semiempirically following the past case histories of earthquakes. This means that there exist reference earthquakes for which the charts, or more specifically their boundaries for liquefaction and no liquefaction, were best validated and most consistent results obtained. The effective number of waves, , is first assessed for such a reference earthquake and is used as . For instance, the liquefaction chart shown in Fig. 2 was best validated against the 1983 Central Japan Sea Earthquake with the corresponding liquefaction and no-liquefaction cases at Akita Port. The effective numbers of waves at various locations at Akita Port during that earthquake were calculated from the site response analysis using the SHAKE code, and the results are shown in Fig. 13. Here, the numbers of soil layers represent the consecutive numbers of soil layers analyzed for various points and depths at this site. It is seen that the values ranged from 3 to 7, with an average of 5. Accordingly, was set to 5. Then, one can perform liquefaction prediction and assessment that simultaneously considers the influence of the waveforms and durations of earthquakes by plotting the cyclic stress ratio or the equivalent acceleration in Fig. 2, which is divided by the wave correction coefficient, , as shown in Fig. 14. Here, the open circles denote example plots with , and the solid circles and triangles represent the corresponding corrected plots for a lower effective number of waves with and for a higher effective number of waves with . The symbol represents the corrected equivalent acceleration, namely, the corrected cyclic stress ratio as divided by the wave correction coefficient . The panel on the bottom shows that the plots can vary, crossing the dividing line between liquefaction and no liquefaction.
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It is necessary to check the accuracy of the wave correction coefficient, . The predicted liquefaction resistances using Eqs. (4) and (5), i.e., the dotted lines in Fig. 11, and the measured liquefaction resistances, i.e., the solid lines in Fig. 11, are plotted as solid circles in Fig. 15. Comparison of the predicted and measured liquefaction resistances confirms the accuracy of the wave correction coefficient, . In Fig. 15, the predictions from a fatigue theory (Annaki and Lee 1977) are also plotted as open circles for comparison. Here, the liquefaction resistances for the irregular waves were predicted using information on the liquefaction resistance curves for the regular waves shown in Fig. 6. Essentially the same degree of accuracy is observed for both theories.
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Verification of the Proposed Method Using Case Histories of Five Major Earthquakes
This section discusses the validity of the proposed new liquefaction prediction and assessment method in light of the past case histories of major earthquakes involving liquefaction and no liquefaction. The basal liquefaction chart for which the proposed method was applied is shown in Fig. 2. The case histories used were (1) the 1983 Central Japan Sea Earthquake with a moment magnitude of 7.8 at Akita Port, (2) 1993 Kushiro Offshore Earthquake with a moment magnitude of 7.6 at Kushiro Port, (3) 1995 Southern Hyogo Prefecture Earthquake with a moment magnitude of 6.9 at Port Island Kobe, (4) 2009 Suruga Bay Earthquake with a moment magnitude of 6.3 at Omaezaki Port, and (5) 2011 Off the Pacific Coast of Tohoku Earthquake with a moment magnitude of 9.0 at Urayasu City, Japan.
The input acceleration used for the 1983 Central Japan Sea Earthquake at Akita Port is shown in Fig. 16. This acceleration represents an outcrop 2E wave that was deconvolved to the rock base, which was at a depth of 7 m from the ground surface, at the site from the observed waveform of the ground surface acceleration there. The site response analysis using the SHAKE code was performed for the soil profiles at the Akita Port. The new method was then applied to the corresponding liquefaction prediction and assessment. The predicted results are shown in Fig. 16. Here, the solid circles represent the liquefied points, and the open circles represent the nonliquefied points. The liquefied and nonliquefied points are based on postearthquake field observations for the sites. The results from the conventional method and the new method with the wave corrections introduced are plotted together in a superimposed manner. It is seen that, regardless of the presence or absence of the wave corrections, both of the predicted results are generally consistent with the liquefaction and no-liquefaction cases.
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The input acceleration used for the 1993 Kushiro Offshore Earthquake at Kushiro Port is shown in Fig. 17. This acceleration was observed at the engineering rock base [ground surface level (G.L.), ] of Kushiro Port. The results of the corresponding liquefaction prediction and assessment, performed in the same way as described above, are shown in Fig. 17. At the observation site, no traces of liquefaction were reported. The predicted results show no liquefaction (Zone IV) and a low possibility of liquefaction (Zone III) regardless of the presence or absence of the wave corrections, and are consistent with the observed results. Closer examination tells us that the predicted results after introducing the wave corrections show higher equivalent accelerations globally and partly approached Zone II with a high possibility of liquefaction. At Kushiro Port, although the liquefaction state was not reached, cyclic mobility that manifests itself in the course of the build-up of excess pore-water pressures in dense sands was reported to take place (Iai et al. 1995). In this respect, the results predicted by the new method appear to be more consistent with the field evidence in cases with no liquefaction but a partly near-liquefied state.
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The acceleration observed at G.L. of through array observation at Port Island Kobe during the 1995 Southern Hyogo Prefecture Earthquake was used as an input for the liquefaction prediction and assessment shown in Fig. 18. At the observation site, traces of liquefaction were confirmed, indicating that liquefaction took place at the site. The results of the corresponding liquefaction prediction and assessment are shown in Fig. 18. All of the predicted results, regardless of the wave corrections, lie in Zone I, showing that liquefaction will occur, and are consistent with the liquefaction cases.
![](/cms/10.1061/(ASCE)GT.1943-5606.0001597/asset/29752b84-7f98-4aab-bda9-760de546c527/assets/images/large/figure18.jpg)
The acceleration observed at the engineering rock base (G.L., ) of Omaezaki Port during the 2009 Suruga Bay Earthquake, and used as an input for the liquefaction prediction and assessment is shown in Fig. 19. As seen in this figure, the seismic motion was in impulsive form, giving rise to a very low effective number of waves, equal to unity. At the observation site, no traces of liquefaction were found, indicating that liquefaction did not take place. The results of the corresponding liquefaction prediction and assessment are shown in Fig. 19. The conventional method predicted that liquefaction will occur or that there is a high possibility of liquefaction. By contrast, the new method predicted significantly lower possibilities of liquefaction, with a major shift in the predictive zones. Thus, the new method showed markedly improved predictive capability and consistency with the no-liquefaction cases.
![](/cms/10.1061/(ASCE)GT.1943-5606.0001597/asset/cce57bcb-4a43-4000-9d2d-1bbf439b6b03/assets/images/large/figure19.jpg)
The acceleration observed adjacent to the Urayasu City during the 2011 Off the Pacific Coast of Tohoku Earthquake, and used as an input for the analysis of the liquefaction is shown in Fig. 20. The Tohoku earthquake had a long duration () that was about 10 times longer than that of the 1995 major Kobe Earthquake. The results of the corresponding liquefaction prediction and assessment are shown in Fig. 20. The predicted results are generally consistent with the observed results for liquefaction and no liquefaction. A closer examination shows that the new method showed increased equivalent accelerations in Zone II, with a high possibility of liquefaction, confirming the accuracy of the predictions in the liquefaction cases. Also, the liquefied point, indicated by the solid triangle in Zone III, which was predicted to have a low possibility of liquefaction by the conventional method, shifted marginally so as to come in contact with the boundary of Zone II, showing a high possibility of liquefaction. These results indicate that the new method has improved predictive capability in liquefaction cases.
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Finally, it is worth investigating the relationships between the effective number of waves and the magnitudes of the five major earthquakes described earlier, as shown in Fig. 21. While there is a tendency for the effective number of waves to increase with increasing magnitude, it is evident that a unique relationship does not exist between and , and in particular, varies considerably for a given earthquake magnitude. This means that the magnitude itself cannot be used to infer the effective number of waves, which has been introduced and validated, to account for the influence of such waveforms and durations of earthquakes on liquefaction.
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Conclusions
This paper has presented and discussed a new simplified liquefaction prediction and assessment method that is capable of considering the influence of irregularities in the waveforms and durations of seismic motions.
The new method adopts the concept of an effective number of waves, which was studied via statistical analysis and validated using the results of a comprehensive set of laboratory liquefaction tests with undrained cyclic torsional shear and constant-volume cyclic simple shear comprising 241 test cases. A total of 11 types of irregular seismic waves were used to clarify this concept, which represents the characteristics of the variety of the waveforms and different numbers of load cycles, as well as their influence on the occurrence of liquefaction in a simple yet workable way.
In the proposed method, liquefaction prediction and assessment can be performed using the wave correction coefficient defined in Eq. (4), together with the site response analysis for calculating the maximum cyclic stress ratios and the effective numbers of waves under the target seismic motions. The validity of the new method was verified with the case histories of five major earthquakes in Japan, namely, the 1983 Central Japan Sea Earthquake, the 1993 Kushiro Offshore Earthquake, the 1995 Southern Hyogo Prefecture Earthquake, the 2009 Suruga Bay Earthquake, and the 2011 Off the Pacific Coast of Tohoku Earthquake. The results demonstrate that the new method has improved predictive capability and accuracy in comparison with the conventional method for cases of liquefaction and no liquefaction.
The proposed new method with the reference effective number of waves has the unique feature that it can be applied to all types of liquefaction charts formulated in terms of the cyclic stress ratio and field measured values, such as SPT -values, CPT -values, and shear-wave velocities. The corresponding procedures were described and explained. The authors sincerely hope that the new simplified method will be widely used for liquefaction prediction and assessment with such influence of the waveforms and durations of earthquakes introduced.
Notation
The following symbols are used in this paper:
- cyclic stress ratio for irregular seismic wave;
- cyclic stress ratio for regular seismic wave;
- cyclic resistance ratio for regular seismic wave with ;
- wave correction coefficient;
- soil relative density;
- gravitational acceleration;
- -value from standard penetration test;
- equivalent -value corresponding to ;
- number of load cycles with constant-amplitude shear stress;
- effective number of waves;
- reference value of ;
- tip resistance from cone penetration test;
- coefficient of uniformity;
- excess pore water pressure;
- shear-wave velocity;
- equivalent acceleration defined by Eq. (2) in terms of cyclic stress ratio;
- proportion of acting shear stress relative to the maximum shear stress;
- shear strain;
- double-amplitude shear strain;
- initial effective vertical stress;
- shear stress;
- constant-amplitude shear stress; and
- maximum shear stress.
Acknowledgments
The authors would like to acknowledge Urayasu City, Japan, for providing the ground data concerning the analysis of the liquefaction at Urayasu City.
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Received: Nov 7, 2015
Accepted: Jun 15, 2016
Published online: Aug 8, 2016
Discussion open until: Jan 8, 2017
Published in print: Feb 1, 2017
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