Resilience Evaluation of Shallow Circular Tunnels Subjected to Earthquakes Using Fragility Functions

: The present work aims to introduce an integrated framework for the resilience evaluation of shallow circular tunnels subjected to earthquakes using fragility and restoration functions. A typical shallow circular tunnel in Shanghai city of China is examined in this work and a corresponding numerical model is established using ABAQUS. Then, a set of ground motions are well chosen to implement large numbers of non-linear numerical analyses so as to determine the lining responses of the tunnel structure with various levels of seismic intensities. According to the above numerical results, fragility functions in terms of the peak ground acceleration ( PGA ) and peak ground velocity ( PGV ) at the free-ﬁeld ground surface are generated, accounting for the main sources of uncertainty, and the direct seismic loss for the examined tunnel is obtained. Moreover, according to the developed fragility functions and the existing empirical tunnel restoration functions, the evolution of the resilience index ( Re ) with various levels of PGA and PGV for the examined tunnel is derived and quantiﬁed. The results indicate that the tunnel resilience will decrease signiﬁcantly as the earthquake intensity measure ( IM ), i.e., PGA or PGV herein, increases. The proposed framework is expected to help city managers support adaptations to seismic hazards with the development of preventive or retroﬁtting measures as part of efforts to provide more resilient metro systems.


Introduction
In recent decades, the increasing intensity and frequency of earthquakes have posed a significant risk to operational tunnels [1].For instance, in China, after the 2008 Wenchuan earthquake, numerous tunnels were reported to have suffered from different degrees of damage [2], causing significant economic losses and casualties.Moreover, tunnels constitute crucial elements of transportation infrastructure worldwide; seismically induced damage of tunnels may thus have substantial consequences on the operation of the global transportation network after a significant event [3].Therefore, a thorough study of the resilience evaluation of tunnels is of paramount importance to the development of better seismic infrastructure planning and interventions.
Seismic resilience describes the capability of a tunnel and associated organizations and communities to mitigate damage induced by earthquake loading [4], these factors constituting the key components in vulnerability and risk analyses for metro systems.Tunnels that are resilient to earthquakes can maintain and even enhance their crucial functionality by responding and adjusting to seismic events.In this sense, resilience can be associated with organizational, technical, social, and economic dimensions [5].Critical infrastructure assessments based on the concept of resilience have been at the forefront of research for decades [6,7] and are gradually being integrated into the design practices and operational procedures of transport infrastructure stakeholders [8,9].
Quantifying infrastructure resilience is typically associated with the so-called resilience indexes, which describe the assets' ability to absorb the effects of damage, adjust to new circumstances, and return to normal after failure [9,10].Moreover, indexes related to the resilience curve, which describes how well a structure recovers after an earthquake event and how quickly it can return to full functionality, are widely used [8][9][10].The resilience assessment frameworks for single and multiple hazards have been developed and applied to a variety of infrastructures, such as hospital facilities [11,12], schools [13,14], transportation networks [9,10], buildings [15,16] and bridges [17,18].These existing works have been conducted with various assumptions and have some limitations [19][20][21]; thus, there is a need for further studies related to the development of more rigorous resilience assessment frameworks for different types of infrastructure.Additionally, there have been recent introductions of resilience considerations for tunnels that account for the effects of extreme surcharge discussed by Huang and Zhang [22]; nevertheless, to the author's best knowledge, such an evaluation framework related to the seismic resilience of tunnels has not been considered in the literature.
To bridge this gap, this study extends the author's previous investigation published at the 4th International Conference on Performance-Based Design in Earthquake Geotechnical Engineering (PBD-IV) [23] to further shed light on the resilience of shallow circular tunnels subjected to earthquakes using fragility functions.This study focuses on the probabilistic seismic resilience evaluation of circular tunnels in typical soft soil areas.The seismic resilience of the examined tunnel is quantified based on the developed fragility functions and existing restoration functions.The effects of various fragility functions proposed by different researchers on tunnels' resilience are also highlighted.The findings of this study are expected to assist consultants, operators, and stakeholders in enhancing seismic risk management as part of the development of more resilient metro systems.

Seismic Resilience Evaluation Framework
Seismic resilience is a helpful measure for investigating a tunnel's ability to withstand various levels of earthquake intensity.In this study, tunnel resilience is assessed by utilizing the following steps, as shown in Figure 1.First, the examined tunnel properties and soil site information are introduced (step (a)).Then, ground motions are well-chosen to cover sufficient variabilities (step (b)).Based on this, a numerical model is developed for the selected soil-tunnel system by ABAQUS, and large numbers of dynamic analyses are conducted (step (c)).Afterwards, the relationship between the examined tunnel's damage index (DI) and selected intensity measure (IM) is determined (step (d)).Following this step, the corresponding fragility functions are proposed in terms of selected IMs (step (e)).Finally, the loss function (step (f)) and seismic resilience curve (step (g)) are developed for the examined tunnel based on the above steps.The above seven steps are introduced in the following parts.

Modelling Soil-Tunnel Configurations
Steps (a), (b), and (c) in Figure 1 are introduced in detail in this section on Modelling Soil-Tunnel Configurations.A typical shield tunnel, located in Shanghai city of China, is used to perform a seismic resilience assessment, as shown in Figure 2. The circular tunnel is built in the soft soil profile, at a depth of 100 m, and lies on the elastic bedrock.This type of tunnel has a radius of 3.10 m, and a lining thickness of 0.35 m.Moreover, its elastic modulus (E c ) is 3.55 GPa, and its Poisson's ratio (v c ) is 0.2.As indicated in Figure 2, this tunnel has a buried depth (h) of 9.0 m; therefore, the tunnel overburden depth ratio (h/d) is equal to 1.45.This is a typical case of a shallow tunnel.

Modelling Soil-Tunnel Configurations
Steps (a), (b), and (c) in Figure 1 are introduced in detail in this section on Modelling Soil-Tunnel Configurations.A typical shield tunnel, located in Shanghai city of China, is used to perform a seismic resilience assessment, as shown in Figure 2. The circular tunnel is built in the soft soil profile, at a depth of 100 m, and lies on the elastic bedrock.This type of tunnel has a radius of 3.10 m, and a lining thickness of 0.35 m.Moreover, its elastic modulus (Ec) is 3.55 GPa, and its Poisson's ratio (vc) is 0.2.As indicated in Figure 2, this tunnel has a buried depth (h) of 9.0 m; therefore, the tunnel overburden depth ratio (h/d) is equal to 1.45.This is a typical case of a shallow tunnel.

Modelling Soil-Tunnel Configurations
Steps (a), (b), and (c) in Figure 1 are introduced in detail in this section on Modelling Soil-Tunnel Configurations.A typical shield tunnel, located in Shanghai city of China, is used to perform a seismic resilience assessment, as shown in Figure 2. The circular tunnel is built in the soft soil profile, at a depth of 100 m, and lies on the elastic bedrock.This type of tunnel has a radius of 3.10 m, and a lining thickness of 0.35 m.Moreover, its elastic modulus (Ec) is 3.55 GPa, and its Poisson's ratio (vc) is 0.2.As indicated in Figure 2, this tunnel has a buried depth (h) of 9.0 m; therefore, the tunnel overburden depth ratio (h/d) is equal to 1.45.This is a typical case of a shallow tunnel.Three soil profiles are chosen and classified as soil type D according to EC8 [24]; they are further referred to as soil deposits D1, D2, and D3 in this work.For all three selected soil profiles, the detailed developments of shear wave velocities (V s ), density (ρ), cohesion (c), and friction angle (ϕ) along the soil height are presented in Figure 3, respectively.Additionally, Figure 4a,b show the typical G-γ-D curves for clayey and sandy layers, respectively.The author's previous work could be used to check more details about the selected soil profiles [23].
Three soil profiles are chosen and classified as soil type D according to EC8 [24]; they are further referred to as soil deposits D1, D2, and D3 in this work.For all three selected soil profiles, the detailed developments of shear wave velocities (Vs), density (ρ), cohesion (c), and friction angle (φ) along the soil height are presented in Figure 3, respectively.Additionally, Figure 4a,b show the typical G-γ-D curves for clayey and sandy layers, respectively.The author's previous work could be used to check more details about the selected soil profiles [23].Figure 5 shows a detailed two-dimensional (2D) finite element model of the studied soil-tunnel configuration generated by the platform ABAQUS.This model has a height of 100 m and a width of 400 m.As for the base boundary of the model, it is simulated as an 'elastic bedrock' using the method of Lysmer and Kuhlemeyer [25] by setting appropriate dashpots, where the selected ground motions are inputted.For the lateral boundaries of the model, a kinematic tie constraint is set to let the opposite vertical sides move at the same time.The tunnel-soil interface is appropriately simulated by a finite sliding hard contact algorithm provided by ABAQUS.The tangential behavior is reflected based on the penalty friction formulation by introducing a commonly used Coulomb frictional model with a friction parameter (μ) equal to 0.6.The response of tunnel lining is modeled Three soil profiles are chosen and classified as soil type D according to EC8 [24]; they are further referred to as soil deposits D1, D2, and D3 in this work.For all three selected soil profiles, the detailed developments of shear wave velocities (Vs), density (ρ), cohesion (c), and friction angle (φ) along the soil height are presented in Figure 3, respectively.Additionally, Figure 4a,b show the typical G-γ-D curves for clayey and sandy layers, respectively.The author's previous work could be used to check more details about the selected soil profiles [23].Figure 5 shows a detailed two-dimensional (2D) finite element model of the studied soil-tunnel configuration generated by the platform ABAQUS.This model has a height of 100 m and a width of 400 m.As for the base boundary of the model, it is simulated as an 'elastic bedrock' using the method of Lysmer and Kuhlemeyer [25] by setting appropriate dashpots, where the selected ground motions are inputted.For the lateral boundaries of the model, a kinematic tie constraint is set to let the opposite vertical sides move at the same time.The tunnel-soil interface is appropriately simulated by a finite sliding hard contact algorithm provided by ABAQUS.The tangential behavior is reflected based on the penalty friction formulation by introducing a commonly used Coulomb frictional model with a friction parameter (μ) equal to 0.6.The response of tunnel lining is modeled Figure 5 shows a detailed two-dimensional (2D) finite element model of the studied soil-tunnel configuration generated by the platform ABAQUS.This model has a height of 100 m and a width of 400 m.As for the base boundary of the model, it is simulated as an 'elastic bedrock' using the method of Lysmer and Kuhlemeyer [25] by setting appropriate dashpots, where the selected ground motions are inputted.For the lateral boundaries of the model, a kinematic tie constraint is set to let the opposite vertical sides move at the same time.The tunnel-soil interface is appropriately simulated by a finite sliding hard contact algorithm provided by ABAQUS.The tangential behavior is reflected based on the penalty friction formulation by introducing a commonly used Coulomb frictional model with a friction parameter (µ) equal to 0.6.The response of tunnel lining is modeled by a simple linear elastic model.A uniform tunnel lining is adopted in the numerical model, focusing the computational efficiency in the analyzed cases.A Mohr-Coulomb model is utilized to capture the non-linear behavior of soil in the dynamic analysis.Each analysis is performed in two consequent steps, i.e., a geostatic step followed by a dynamic analysis step.The first step is conducted to build the geostatic stress equilibrium within the numerical model.In contrast, the acceleration time history is introduced via dashpots at the model's base in the second step.More details about the numerical model development could be checked in the author's previous work [23].
model, focusing the computational efficiency in the analyzed cases.A Mohr-Coulomb model is utilized to capture the non-linear behavior of soil in the dynamic analysis.Each analysis is performed in two consequent steps, i.e., a geostatic step followed by a dynamic analysis step.The first step is conducted to build the geostatic stress equilibrium within the numerical model.In contrast, the acceleration time history is introduced via dashpots at the model's base in the second step.More details about the numerical model development could be checked in the author's previous work [23].It is very important to choose a set of ground motions that cover a high level of uncertainty within the seismic fragility analysis of any element at risk so as to perform an accurate seismic risk assessment.Table 1 shows the general properties of the selected 12 seismic ground motions in this work, which are provided by the Pacific Earthquake Engineering Research Strong Motion Database (10 April 2020, https://ngawest2.berkeley.edu).These ground motions are scaled from 0.1 g to 1.0 g, with a gradient of 0.1 g, and then applied in the numerical modeling.More information about the selection of the adopted seismic records can be found in the author's work for the PBD-IV [23].

Generation of Fragility Functions
As illustrated in Equation ( 1), most fragility functions could be expressed using a cumulative lognormal probability distribution function [15][16][17]: It is very important to choose a set of ground motions that cover a high level of uncertainty within the seismic fragility analysis of any element at risk so as to perform an accurate seismic risk assessment.Table 1 shows the general properties of the selected 12 seismic ground motions in this work, which are provided by the Pacific Earthquake Engineering Research Strong Motion Database (https://ngawest2.berkeley.eduaccessed on 10 April 2020).These ground motions are scaled from 0.1 g to 1.0 g, with a gradient of 0.1 g, and then applied in the numerical modeling.More information about the selection of the adopted seismic records can be found in the author's work for the PBD-IV [23].

Generation of Fragility Functions
As illustrated in Equation ( 1), most fragility functions could be expressed using a cumulative lognormal probability distribution function [15][16][17]: where P(ds ≥ ds j |IM) represents the exceedance probability of a specific damage state, i.e., DS or ds, under an earthquake intensity level, the latter being described through the earthquake intensity measure IM, i.e., PGA or PGV in this work; Φ(•) represents the cumulative distribution function; IM mj stands for the mean value of IM needed to induce the j th ds; and β tot stands for the total standard deviation, which can be calculated through the combination of three main sources of uncertainty, as illustrated in Equation ( 2): where β ds is the uncertainty involved in defining various damage states; β C is used to quantify the uncertainty associated with the response of the structure (seismic capacity); and β D is utilized to describe the uncertainty originating from the ground motions (seismic demand).The parameters of β ds and β C are assumed to be 0.4 and 0.3, respectively [26].
A damage index (DI) is utilized to appropriately characterize various damage states and is defined using the ratio of the actual (M) over the capacity (M Rd ) bending moment of the tunnel lining cross-section [26].On this basis, the capacity (M Rd ) bending moment of the tunnel lining is assessed by a section analysis [26] according to the material and geometric characteristics of the lining, taking into account the actual axial forces (N) and bending moments (M).Five damage states are introduced in Table 2.

Direct Seismic Loss Analyisis
By using the above-proposed fragility functions, the probabilities of exceeding the particular damage states can be calculated.Subsequently, the direct seismic losses (S loss s) of tunnels owing to structural damage after earthquake events can be evaluated using the following equation [27]: where S loss is the average estimated cost of repairing the tunnel, given the specific level of earthquake intensity measure, IM; R c stands for the cost of tunnel replacement per meter; L is the length of the examined tunnels (L is set as 1 m in this study); the index j stands for the jth damage state (DS j ), and the index n represents the total number of damage states; R j represents the repair ratio, which is the fraction of R c necessary to repair the jth damage state; P[DS j |IM] represents the probability that the tunnel is located at each damage state j and seismic intensity level (IM), as presented in the following equations based on the fragility functions: P DS j I M = P ds > DS j I M , when j = 4. ( More specifically, the replacement cost of the examined tunnel per meter (R c ) is assumed to be 1,000,000 RMB/m in this study, which is a preliminary estimate of the direct costs based on the construction cost of tunnels in China.The repair ratios (R j ) utilized in this work were put forward by Werner et al. [28] for tunnels, as shown in Table 3.For instance, a minor damage state of the tunnel indicates that the repair cost is equal to 10% of the total replacement cost.An example of using fragility functions under a specific seismic IM to calculate the direct seismic loss of tunnels is shown in Figure 6.instance, a minor damage state of the tunnel indicates that the repair cost is equal to 10% of the total replacement cost.An example of using fragility functions under a specific seismic IM to calculate the direct seismic loss of tunnels is shown in Figure 6.

Seismic Resilience Index Assessment Procedure
Resilience (Re) is a term used to describe the ability of tunnels to recover after being subjected to seismic damage.The most widely used analytical definition is adopted in this work.The following formula can be used to calculate Re [10,13]: where Q(t) represents the tunnel functionality at time t under the functionality recovery function, t0 is the earthquake occurrence time (t0 is set as 0 in this study), and th is the investigated time point.As defined in Equation (3), the resilience index (Re) can be graphically illustrated, as shown in Figure 7.
Figure 6.An illustrative case of using the fragility function for a given IM to calculate the direct seismic loss of tunnels.

Seismic Resilience Index Assessment Procedure
Resilience (Re) is a term used to describe the ability of tunnels to recover after being subjected to seismic damage.The most widely used analytical definition is adopted in this work.The following formula can be used to calculate Re [10,13]: where Q(t) represents the tunnel functionality at time t under the functionality recovery function, t 0 is the earthquake occurrence time (t 0 is set as 0 in this study), and t h is the investigated time point.As defined in Equation (3), the resilience index (Re) can be graphically illustrated, as shown in Figure 7.The seismic resilience index (Re) of the examined tunnel exposed to a certain IM level can be derived using the fragility and restoration functions.The latter describes the speed of restoration of functionality for the different DSs and the probabilities of occurrence for each DS, as discussed in the following sections.Hence, the tunnel functionality at time t can be computed as Equation (7) [14,15]: where Q[DSj|t] represents the function to restore the functionality of the tunnel at time t and damage state j, and P[DSj|IM] stands for the conditional probability of a damage state j for an event with a given IM, which can be calculated by Equations ( 4) and (5).

Restoration Function and Time
For the following seismic resilience analysis, because of the lack of a specific restoration function for the studied tunnel, the empirical ones provided by FEMA [27] are used in this work, as presented in Figure 8 in terms of minor, moderate, and extensive damage, derived based on the results from the experts' surveys.It is noted that there is a need for the development of rigorous restoration models that will account more accurately for critical parameters, such as the availability of relevant sources and funds, management approaches in constructions and repairs, and maintenance strategies.The seismic resilience index (Re) of the examined tunnel exposed to a certain IM level can be derived using the fragility and restoration functions.The latter describes the speed of restoration of functionality for the different DSs and the probabilities of occurrence for each DS, as discussed in the following sections.Hence, the tunnel functionality at time t can be computed as Equation (7) [14,15]: where Q[DS j |t] represents the function to restore the functionality of the tunnel at time t and damage state j, and P[DS j |IM] stands for the conditional probability of a damage state j for an event with a given IM, which can be calculated by Equations ( 4) and (5).

Restoration Function and Time
For the following seismic resilience analysis, because of the lack of a specific restoration function for the studied tunnel, the empirical ones provided by FEMA [27] are used in this work, as presented in Figure 8 in terms of minor, moderate, and extensive damage, derived based on the results from the experts' surveys.It is noted that there is a need for the development of rigorous restoration models that will account more accurately for critical parameters, such as the availability of relevant sources and funds, management approaches in constructions and repairs, and maintenance strategies.The seismic resilience index (Re) of the examined tunnel exposed to a certain IM level can be derived using the fragility and restoration functions.The latter describes the speed of restoration of functionality for the different DSs and the probabilities of occurrence for each DS, as discussed in the following sections.Hence, the tunnel functionality at time t can be computed as Equation (7) [14,15]: where Q[DSj|t] represents the function to restore the functionality of the tunnel at time t and damage state j, and P[DSj|IM] stands for the conditional probability of a damage state j for an event with a given IM, which can be calculated by Equations ( 4) and (5).

Restoration Function and Time
For the following seismic resilience analysis, because of the lack of a specific restoration function for the studied tunnel, the empirical ones provided by FEMA [27] are used in this work, as presented in Figure 8 in terms of minor, moderate, and extensive damage, derived based on the results from the experts' surveys.It is noted that there is a need for the development of rigorous restoration models that will account more accurately for critical parameters, such as the availability of relevant sources and funds, management approaches in constructions and repairs, and maintenance strategies.According to the above considerations, two parameters, i.e., IM mi and β tot , are required to derive the corresponding fragility functions.The value of IM mi for PGA or PGV concerning the various DSs is computed using a regression analysis for the nonlinear numerical results.Particularly in this study, a traditional linear regression analysis is adopted using the natural logarithm of the DI and IM as the variables.As shown in Figure 9a,b, the different data points (360 in total) stand for the corresponding damage indexes under increasing levels of PGA, while the solid blue line indicates the regression fit curve for these Ln(DI)-Ln(IM) datasets.It is noted that IM mi is computed based on the regression fit equation with the different thresholds of DS. β D is calculated as the dispersion of the different data points with regard to the curve of regression fit [26], and the total lognormal standard deviation β tot is calculated using Equation ( 2).The detailed fragility function parameters in terms of IM mi and β tot are also presented in Figure 9.

Derivation of Fragility Function Parameters
According to the above considerations, two parameters, i.e., IMmi and βtot, are required to derive the corresponding fragility functions.The value of IMmi for PGA or PGV concerning the various DSs is computed using a regression analysis for the nonlinear numerical results.Particularly in this study, a traditional linear regression analysis is adopted using the natural logarithm of the DI and IM as the variables.As shown in Figure 9a,b, the different data points (360 in total) stand for the corresponding damage indexes under increasing levels of PGA, while the solid blue line indicates the regression fit curve for these Ln(DI)-Ln(IM) datasets.It is noted that IMmi is computed based on the regression fit equation with the different thresholds of DS. βD is calculated as the dispersion of the different data points with regard to the curve of regression fit [26], and the total lognormal standard deviation βtot is calculated using Equation ( 2).The detailed fragility function parameters in terms of IMmi and βtot are also presented in Figure 9.

Development of Fragility Functions
Based on the derived fragility parameters, the corresponding fragility functions can be developed using Equation (1). Figure 10a presents the PGA-based fragility functions for the examined tunnel in soft soil.Naturally, the exceedance probability of damage would increase with increasing PGA.As the value of PGA is lower than 0.3 g, the probability of extensive damage is negligible, which means that the examined shallow tunnel may withstand this level of earthquake intensity well, practically with no damage.The minor and moderate damage probabilities are 15% and 2%, respectively.When PGA equals 0.4 g, the exceedance probabilities for minor, moderate, and extensive damage will increase to 60%, 22%, and 5%, respectively.In comparison, as the value of PGA increases to near 1.0 g, there is a 97% probability that the tunnel will be exposed to minor damage.The relevant possibilities for moderate or extensive damage are 83% and 52%.The latter observations highlight the significant importance of sufficient seismic designs for shield tunnels in similar sites.Similar conclusions can also be obtained for the fragility functions developed in terms of PGV at the ground surface.

Development of Fragility Functions
Based on the derived fragility parameters, the corresponding fragility functions can be developed using Equation (1). Figure 10a presents the PGA-based fragility functions for the examined tunnel in soft soil.Naturally, the exceedance probability of damage would increase with increasing PGA.As the value of PGA is lower than 0.3 g, the probability of extensive damage is negligible, which means that the examined shallow tunnel may withstand this level of earthquake intensity well, practically with no damage.The minor and moderate damage probabilities are 15% and 2%, respectively.When PGA equals 0.4 g, the exceedance probabilities for minor, moderate, and extensive damage will increase to 60%, 22%, and 5%, respectively.In comparison, as the value of PGA increases to near 1.0 g, there is a 97% probability that the tunnel will be exposed to minor damage.The relevant possibilities for moderate or extensive damage are 83% and 52%.The latter observations highlight the significant importance of sufficient seismic designs for shield tunnels in similar sites.Similar conclusions can also be obtained for the fragility functions developed in terms of PGV at the ground surface.

Seismic Loss Assessment
Figure 11a,b provide the calculated direct seismic loss curves for the examined tunnel in terms of PGA and PGV, respectively.The fundamental trends of seismic loss curves are in line with the corresponding fragility functions.Using the derived loss curves, the repair cost of each tunnel ring (per meter) could be calculated for various seismic levels.For example, suppose a metro line is exposed to an earthquake intensity of PGA = 0.5 g.In that case, the total repair cost for the examined tunnel could easily be found to be 180,000 RMB from Figure 11a, indicating that rather essential repairs would be required for each tunnel segment.Similar conclusions may be drawn by examining Figure 11b, where the IM is given in terms of PGV.In this way, the proposed direct seismic loss curves can be employed in the quantitative risk assessment of the metro tunnel network subjected to seismic loading.

Seismic Loss Assessment
Figure 11a,b provide the calculated direct seismic loss curves for the examined tunnel in terms of PGA and PGV, respectively.The fundamental trends of seismic loss curves are in line with the corresponding fragility functions.Using the derived loss curves, the repair cost of each tunnel ring (per meter) could be calculated for various seismic levels.For example, suppose a metro line is exposed to an earthquake intensity of PGA = 0.5 g.In that case, the total repair cost for the examined tunnel could easily be found to be 180,000 RMB from Figure 11a, indicating that rather essential repairs would be required for each tunnel segment.Similar conclusions may be drawn by examining Figure 11b, where the IM is given in terms of PGV.In this way, the proposed direct seismic loss curves can be employed in the quantitative risk assessment of the metro tunnel network subjected to seismic loading.

Seismic Loss Assessment
Figure 11a,b provide the calculated direct seismic loss curves for the examined tunnel in terms of PGA and PGV, respectively.The fundamental trends of seismic loss curves are in line with the corresponding fragility functions.Using the derived loss curves, the repair cost of each tunnel ring (per meter) could be calculated for various seismic levels.For example, suppose a metro line is exposed to an earthquake intensity of PGA = 0.5 g.In that case, the total repair cost for the examined tunnel could easily be found to be 180,000 RMB from Figure 11a, indicating that rather essential repairs would be required for each tunnel segment.Similar conclusions may be drawn by examining Figure 11b, where the IM is given in terms of PGV.In this way, the proposed direct seismic loss curves can be employed in the quantitative risk assessment of the metro tunnel network subjected to seismic loading.

Tunnel Functionality Assessment
According to Equation (3), the tunnel functionality Q(t) at time t is calculated by the developed fragility functions and functionality restoration functions [27].Figure 12a,b present the influences of five different values of PGA (0.2, 0.4, 0.6, 0.8, and 1.0 g) and five different values of PGV (0.2, 0.4, 0.6, 0.8, and 1.0 m/s) on the development of tunnel functionality, Q(t).As expected, the damage induced by a lower seismic intensity (PGA or PGV) seems to be more easily recovered from, indicating a higher resilience index (Re) with lower PGA and PGV for the studied tunnel.3), the tunnel functionality Q(t) at time t is calculated by developed fragility functions and functionality restoration functions [27].Figure 1 present the influences of five different values of PGA (0.2, 0.4, 0.6, 0.8, and 1.0 g) and different values of PGV (0.2, 0.4, 0.6, 0.8, and 1.0 m/s) on the development of tunnel f tionality, Q(t).As expected, the damage induced by a lower seismic intensity (PG PGV) seems to be more easily recovered from, indicating a higher resilience index with lower PGA and PGV for the studied tunnel.

Development of the Resilience Index
Figure 13a,b show the resilience index (Re)'s evolution for the studied tunnel u the different PGA and PGV values, respectively.Naturally, it is clearly demonstrated the seismic resilience index of tunnels decreases gradually when the PGA or PGV creases.More specifically, as the PGA is ranged between 0.0 g and 1.0 g, the resilien tunnels is found to remain at a level between 0.87 and 0.99.It is more significant in case of PGV, for it is indicated that the resilience of tunnels maintains a high level betw 0.95 and 0.99 when the PGV is ranged between 0.0 m/s and 1.0 m/s.From the above ysis, it is concluded that the examined tunnel is generally good in terms of seismic r ence.Nevertheless, the critical roles of adequate seismic design of the tunnel structure rapid recovery measures at the post-earthquake event in case of severe seismic intens have been demonstrated.

Development of the Resilience Index
Figure 13a,b show the resilience index (Re)'s evolution for the studied tunnel under the different PGA and PGV values, respectively.Naturally, it is clearly demonstrated that the seismic resilience index of tunnels decreases gradually when the PGA or PGV increases.More specifically, as the PGA is ranged between 0.0 g and 1.0 g, the resilience of tunnels is found to remain at a level between 0.87 and 0.99.It is more significant in the case of PGV, for it is indicated that the resilience of tunnels maintains a high level between 0.95 and 0.99 when the PGV is ranged between 0.0 m/s and 1.0 m/s.From the above analysis, it is concluded that the examined tunnel is generally good in terms of seismic resilience.Nevertheless, the critical roles of adequate seismic design of the tunnel structure and rapid recovery measures at the post-earthquake event in case of severe seismic intensities have been demonstrated.

Tunnel Functionality Assessment
According to Equation (3), the tunnel functionality Q(t) at time t is calculated by the developed fragility functions and functionality restoration functions [27].Figure 12a,b present the influences of five different values of PGA (0.2, 0.4, 0.6, 0.8, and 1.0 g) and five different values of PGV (0.2, 0.4, 0.6, 0.8, and 1.0 m/s) on the development of tunnel functionality, Q(t).As expected, the damage induced by a lower seismic intensity (PGA or PGV) seems to be more easily recovered from, indicating a higher resilience index (Re) with lower PGA and PGV for the studied tunnel.

Development of the Resilience Index
Figure 13a,b show the resilience index (Re)'s evolution for the studied tunnel under the different PGA and PGV values, respectively.Naturally, it is clearly demonstrated that the seismic resilience index of tunnels decreases gradually when the PGA or PGV increases.More specifically, as the PGA is ranged between 0.0 g and 1.0 g, the resilience of tunnels is found to remain at a level between 0.87 and 0.99.It is more significant in the case of PGV, for it is indicated that the resilience of tunnels maintains a high level between 0.95 and 0.99 when the PGV is ranged between 0.0 m/s and 1.0 m/s.From the above analysis, it is concluded that the examined tunnel is generally good in terms of seismic resilience.Nevertheless, the critical roles of adequate seismic design of the tunnel structure and rapid recovery measures at the post-earthquake event in case of severe seismic intensities have been demonstrated.

Effects of Different Fragility Functions on Tunnel Resilience
A crucial issue for the resilience evaluation of tunnels is the selection of appropriate fragility functions [29][30][31].Indeed, the use of different fragility functions may lead to distinct probabilities of being in a particular damage state and hence may affect the resilience index estimated for an examined tunnel.To highlight this issue, an example is provided to study the effects of different fragility functions on tunnel resilience.More specifically, the analytical fragility functions provided through this study, Argyroudis and Pitilakis [26] and Argyroudis et al. [32], as well as the empirical fragility functions provided by ALA [33], are used to compute the resilience index Re for the examined case.
Figure 14 illustrates the variation of the resilience index (Re) with increasing levels of the seismic intensity measure (PGA), as computed for the examined soil-tunnel configurations by employing different fragility functions.Evidently, a significant scatter is observed by comparing the Re computed for different levels of seismic IM when using different fragility functions.In particular, for a specific level of seismic intensity, the use of the empirical fragility functions provided by ALA [33] leads to the highest values of Re compared to the values computed when using the analytical fragility functions.On the contrary, the lowest Re values are obtained when using the analytical fragility functions presented by Argyroudis and Pitilakis [26].These observations are attributed to different modelling approaches and assumptions utilized to generate the selected fragility functions.The empirical fragility functions provided by ALA [33] are derived using reports of actual damage of tunnels from past earthquakes as well as expert judgements.The numerical fragility functions provided by Argyroudis and Pitilakis [26] are developed through a couple of numerical analyses of soil-tunnel configurations, with the seismic loading being simulated by employing a quasi-static method.The numerical fragility functions proposed by Argyroudis et al. [32] are generated according to the results of a set of non-linear numerical simulations considering soil-structure interaction phenomena in a more rigorous fashion.Finally, the analytical fragility functions provided by this study are proposed by employing the results of non-linear dynamic analyses of the soil-tunnel configuration, considering the effects of local soil conditions of Shanghai city.Differences in the assumptions made regarding the geometrical properties of the soil-tunnel configuration, the implemented soil constitutive models, and the considered ground motion characteristics may have also affected the computed fragilities of the examined tunnels, hence affecting the computed resilience index of the examined configurations.The above discrepancies reveal the need for further investigation of the seismic fragility and resilience of tunnels.

Conclusions
The present work aimed to assess the resilience of shallow circular tunnels in soft soil areas exposed to earthquakes based on derived fragility functions.The following conclusions can be obtained through the above analyses: (1) The exceedance probabilities, direct seismic losses, and seismic resilience indexes of 0 0 .20.4 0 .60.8 1 PGA(g) 0.7 0.8 0.9 1 1.1 ALA [33] Argyroudis and Pitilakis [26] Argyroudis et al. [32] This study

Figure 1 .
Figure 1.Proposed framework to evaluate the seismic resilience of tunnels.

Figure 2 .
Figure 2. Diagrammatic sketch for the examined circular tunnel (not to scale).

Figure 1 .
Figure 1.Proposed framework to evaluate the seismic resilience of tunnels.

Figure 1 .
Figure 1.Proposed framework to evaluate the seismic resilience of tunnels.

Figure 2 .
Figure 2. Diagrammatic sketch for the examined circular tunnel (not to scale).

Figure 2 .
Figure 2. Diagrammatic sketch for the examined circular tunnel (not to scale).

Figure 3 .
Figure 3. Geotechnical parameters of the examined soil profiles.

Figure 3 .
Figure 3. Geotechnical parameters of the examined soil profiles.

Figure 3 .
Figure 3. Geotechnical parameters of the examined soil profiles.

Figure 7 .
Figure 7. Definition of the resilience index (Re).

Figure 7 .
Figure 7. Definition of the resilience index (Re).

Figure 9 .
Figure 9. Evolution of the DI with (a) PGA and (b) PGV at the free-field ground surface.

Figure 9 .
Figure 9. Evolution of the DI with (a) PGA and (b) PGV at the free-field ground surface.

Figure 10 .
Figure 10.Developed fragility functions by (a) PGA and (b) PGV at the ground surface.

Figure 11 .Figure 10 .
Figure 11.Direct seismic loss of the examined tunnel in terms of (a) PGA and (b) PGV at the freefield ground surface.

Figure 10 .
Figure 10.Developed fragility functions by (a) PGA and (b) PGV at the ground surface.

Figure 11 .Figure 11 .
Figure 11.Direct seismic loss of the examined tunnel in terms of (a) PGA and (b) PGV at the freefield ground surface.

Figure 12 .
Figure 12.Functionality recovery function of the examined tunnel in terms of (a) PGA and (b) at free-field ground surface.

ReFigure 12 .
Figure 12.Functionality recovery function of the examined tunnel in terms of (a) PGA and (b) PGV at free-field ground surface.

Figure 12 .
Figure 12.Functionality recovery function of the examined tunnel in terms of (a) PGA and (b) PGV at free-field ground surface.

ReFigure 13 .
Figure 13.Resilience index Re of the examined tunnel in terms of (a) PGA and (b) PGV at the free-field ground surface.

15 Figure 14 .
Figure 14.Resilience index (Re) of the examined tunnel using different empirical and numerical fragility functions.

Figure 14 .
Figure 14.Resilience index (Re) of the examined tunnel using different empirical and numerical fragility functions.
Figure 6.An illustrative case of using the fragility function for a given IM to calculate the direct seismic loss of tunnels.