Application of the Incremental Modal Pushover Analysis to Bridges Subjected to Near-Fault Ground Motions

: Near-fault events can cause severe damage to civil structures, including bridges. Many studies have demonstrated that the seismic assessment is not straightforward. Usually, dealing with near-fault ground motion, the structural analysis is performed using Nonlinear Response-History Analysis (NRHA) but in the last years, many authors have tested existing pushover-based procedures originally developed and validated using far-field events. Between those procedures, the Incremental Modal Pushover Analysis (IMPAb) is a pushover-based procedure speciﬁcally developed for bridges that, in this work, was applied to a case study considering near-fault pulse-like ground motion records. The records were analyzed and selected from the European Strong Motion Database. In the paper the results obtained with IMPAb together with other standard pushover procedures, are compared with NRHA and incremental dynamic analyses; the vertical component of the motion has been also considered. Results obtained with the bridge case study demonstrate that the vertical seismic action has a minor inﬂuence on the structural response and that IMPAb is conﬁrmed as a very e ﬀ ective pushover-based method that can be applied also for near-fault events. From Figures 7–9, the structural response to each GM is plotted in terms of deck displacement (transversal displacement of the deck at Pier 1, Pier 2 and Pier 3) and the variation of the axial load on each pier. The axial load variation is useful to evaluate the relevance of the vertical component of the GM in terms of axial load-bending moment interaction (the hinge of the piers are PM being P = axial load and M = bending moment) and therefore for the structural response; in a pushover analysis this loading variation cannot be considered adopting procedures such as SPA, UPA or MPA. In all the cited pushover methods the analysis is performed starting from a preliminary nonlinear step in which the vertical static loads are imposed. As already discussed in the introduction, in a preliminary phase of this work, the use of EMPA (a modal pushover that includes also the vertical component of the seismic action) as an alternative to MPA was evaluated. This modiﬁcation of the IMPAb was discarded because the results, using MPA or EMPA were very similar as discussed below.


Introduction
Near-field ground motions (NF) differ from ordinary (far-field) ground motions. The proximity to the fault renders the effect of the global displacements and the mutual displacements of the opposite sides of the fault very evident in the records: (i) the vertical motion component maximum values often exceeds the horizontal component [1]; long period velocity pulses can be generated by (ii) earthquake directivity and (iii) fling-step [2], (iv) differential input displacements at the base of the piers [3].
For (i), in structures prone to axial force variation, the combined effect of horizontal and vertical motions can bring to severe structural demand [4].
Case (ii) happens due to the focusing of wave energy along the fault in the direction of rupture, when this latter propagates towards the site (forward directivity) and when the velocity of propagation is slightly slower than the shear wave velocity, causing the seismic energy to arrive in a large pulse of motion [5]. In this case, the pulses in the velocity time series are generally double-sided, and they are stronger in the component of motion normal to the fault strike.
Case (iii) (fling-step) occurs when the earthquake causes major surface rupture. In this case, there is a slow increase of stresses in the earth crust over long periods of time. Then, the stresses are

Short Description of IMPAb Procedure
It is assumed that NRHA represents the "correct" response evaluation, even for NF input. The incremental modal pushover analysis for bridges (IMPAb) [18] is carried out and results are compared to IDAs. IMPAb requires the execution of several pushover analyses according to two different load patterns: a uniform loading profile (UPA) and a modal pushover analysis (MPA) according to the procedure presented in [16,17]. As previously mentioned, the use of EMPA (which includes vertical action) instead of MPA was tested and verified as irrelevant for the scope of the analysis. In EMPA the seismic excitation vector is the sum of three terms, each one corresponding to the components of the accelerogram record. The pushover capacity curve is obtained taking into account the contributions of the cited excitation vector in the considered degrees of freedom (transversal and vertical displacement): two capacity curves were recorded in a single pushover analysis of each mode (the dominant modes associated with the selected directions) and the component along the investigated direction (the transversal for the case study discussed herein) were successively combined according to the SRSS rule in order to obtain the final capacity curve. Nonetheless, the prediction of the structural response of the bridge with EMPA, also for NF events, is close to MPA (the same conclusion is discussed in [19] for the case study performed with FF events) and therefore the original version of IMPAb, developed and tested considering far-field ground motions (FF), was tested and discussed herein and validated in case of NF.
The irrelevance of the vertical input in the pushover analysis, according to the scope and the results of this paper, is discussed in Section 4.
In addition, in this work a standard pushover analysis (SPA), with a load profile proportional to the dominant modal shape has been performed to compare results from different pushover procedures with NRHA. The IMPAb procedure can be summarized in the following main steps: Combining what obtained according to a combination rule (e.g., CQC or SRSS) a performance point that can be considered "multimodal" (P.P.m,i) can be defined.
Therefore, IMPAb requires to perform an incremental modal pushover analysis (IMPA) and an incremental UPA (IUPA). Afterwards, in order to obtain a univocal capacity curve, for each intensity step i, the IMPAb procedure requires to evaluate the P i,IMPAb (Figure 1) according to (1). The capacity curve obtained is therefore an envelope of the results obtained from UPA and MPA.
being: u r,i,MPA the displacement at the P.P.m,i obtained performing MPA; V b,i,MPA the base shear at the P.P.m,i obtained performing MPA; u r,i,UPA the displacement at the P.P.i obtained performing UPA; V b,i,UPA the base shear at the P.P.i obtained performing UPA.
The seismic demand is expressed in terms of Response Spectrum (RS): a RS can be selected and scaled according to different criteria. In the application discussed herein the RS has been derived from the set of near-fault ground motion records selected ( § 3.2). The RS have been linearly scaled to match the desired intensity range.
Combining what obtained according to a combination rule (e.g., CQC or SRSS) a performance point that can be considered "multimodal" (P.P.m,i) can be defined. Therefore, IMPAb requires to perform an incremental modal pushover analysis (IMPA) and an incremental UPA (IUPA). Afterwards, in order to obtain a univocal capacity curve, for each intensity step i, the IMPAb procedure requires to evaluate the Pi,IMPAb (Figure 1) according to (1). The capacity curve obtained is therefore an envelope of the results obtained from UPA and MPA.

The Case Study
The case study selected is a bridge with a straight deck having a total length of 200 m with four equal spans of 50 m ( Figure 2). The case study has been adopted in many previous works published by many authors since the 1990s [21], and also in a recent work in which the IMPAb [18] has been presented. The bridge is located in Reggio Calabria, Italy, but since in this work we used the strong ground motion records of 2016 Central Italy earthquakes, the actual location of the bridge can be considered Norcia, Italy. The deck of the bridge consists of 14-m-wide pre-cast concrete box girder supported by piers through bearings locked in the transverse direction and, at the abutments, through elastomeric bearings (movement in the longitudinal direction is allowed at the abutments, but transverse displacements are restrained).
The three circular piers (P1, P2 and P3), have different heights and a diameter of 2.5 m. The bridge was designed, according to Eurocode 8, using concrete C20/25 and steel B450C; C20/25 has a characteristic compressive cylindric strength of 20 MPa and the B450 a characteristic yield strength of 450 MPa. The design of the bridge was done considering a seismic action with a design peak ground acceleration of 0.35 g and a behavior factor q = 3.0. The design loads adopted for dimensioning the bridge structural elements are listed in Table 1.
The response of the bridge model was estimated through the employment of nonlinear static and dynamic analyses. The dynamic analyses were performed adopting a set of ground motions (GM) selected according to the criteria described in §3.2; from the set of ground motions, a median response spectra (RSm) was defined. The GMs were used to perform the NRHAs as well as their mean spectrum (RSm) were used for the purpose of evaluating the pushover-based procedure (the performance point is evaluated, for each intensity level, adopting RSm for the seismic demand).
In this paper, ( §4) analysis results are presented in terms of deformed shape of the bridge in transverse direction and bridge capacity curve (i.e., monitoring point displacement versus seismic intensity).
ground motion records of 2016 Central Italy earthquakes, the actual location of the bridge can be considered Norcia, Italy. The deck of the bridge consists of 14-m-wide pre-cast concrete box girder supported by piers through bearings locked in the transverse direction and, at the abutments, through elastomeric bearings (movement in the longitudinal direction is allowed at the abutments, but transverse displacements are restrained).

Selection of Near-Fault Records
The seismic events that hit Italy in 2016 and 2017, known as the Central Italy earthquakes, had been a series of four seismic events occurred in Italy between August and October 2016 [22] with minor events in January 2017. The two major earthquakes were those that occurred on August 24 and October 30, 2016 with magnitudes Mw = 6 and 6.5, respectively. In both cases, many seismic stations close to the epicenters recorded the strong ground motion. In some cases, the records presented typical near-fault pulse-like behavior, as highlighted both in the joint report written by the ReLUIS-INGV Workgroup [23] and reported in the European Strong Motion Database [24]. Table 2 reports the ground motion parameters of the selected records for August 24. The Joyner and Boore distance (R jb ) is the distance from the fault surface projection, and it is reported together with the epicentral distance (R epi ).
The characteristics of the main events were reported by many authors. The study by Luzi et al. [25] reports, among the other pieces of information, the strike of the causative fault of 156 degrees with respect to the North-South direction for the event of August 24. According to these indications, the horizontal records were rotated in order to obtain the Fault Normal and Fault Parallel components of the ground motion. Figure 3 reports the Fault Normal components of the acceleration time series of the selected near-fault ground motion records.  Figure 4 reports the velocity time series (black plots) of the FN components of the 6 seismic stations selected among those which recorded the strong ground motion on 24 August 2016. For each time series, the pulses (red plots) were extracted using the procedure provided by Baker [26]. This method allows to also evaluate the period T p of the pulse. In addition, the peak-to-peak velocity, as given by the difference between the two peaks in one cycle of motion, was evaluated and reported for each record. This parameter can be more useful than PGV because generally, the pulses generated during near-fault strong motion are double-sided [27].
Appl. Sci. 2020, 10, x FOR PEER REVIEW 6 of 19 components of the ground motion. Figure 3 reports the Fault Normal components of the acceleration time series of the selected near-fault ground motion records.  Figure 4 reports the velocity time series (black plots) of the FN components of the 6 seismic stations selected among those which recorded the strong ground motion on August 24, 2016. For each time series, the pulses (red plots) were extracted using the procedure provided by Baker [26]. This method allows to also evaluate the period Tp of the pulse. In addition, the peak-to-peak velocity, as given by the difference between the two peaks in one cycle of motion, was evaluated and reported for each record. This parameter can be more useful than PGV because generally, the pulses generated during near-fault strong motion are double-sided [27]. stations selected among those which recorded the strong ground motion on August 24, 2016. For each time series, the pulses (red plots) were extracted using the procedure provided by Baker [26]. This method allows to also evaluate the period Tp of the pulse. In addition, the peak-to-peak velocity, as given by the difference between the two peaks in one cycle of motion, was evaluated and reported for each record. This parameter can be more useful than PGV because generally, the pulses generated during near-fault strong motion are double-sided [27].

Modeling
The software used to model the bridge was SAP2000 NL, v. 21 [28]; the structural scheme used is the same reported in detail in [29] where the case study model was introduced.
The model ( Figure 5) has been developed according to Pacific Earthquake Engineering Research

Modeling
The software used to model the bridge was SAP2000 NL, v. 21 [28]; the structural scheme used is the same reported in detail in [29] where the case study model was introduced.
The model ( Figure 5) has been developed according to Pacific Earthquake Engineering Research (PEER) guidelines [30] and its properties ideally represent the mass distribution, strength, stiffness and deformability of the real bridge. Following the procedure proposed in [30], piers and girders supporting the deck were modelled by 3D frame elements; the box-girder cross section was defined using the SAP 2000 Section Designer that allows to correctly model the real geometry described in Figure 2.
The fiber hinges were defined by moment-rotation curves calculated using a fiber-based model of the cross-section according to the reinforcement details at the hinge locations. The constitutive model adopted for the concrete (both unconfined and confined) is the Mander's model and the rebar was considered consistently with the code parameters: fy = 450 Mpa, Es = 210000 Mpa, fu = 540 Mpa. More complex models can be used to describe specific cyclic behavior of RC piers [32] also in the presence of corrosion [33].

Modal Properties
According to the IMPAb procedure, a modal analysis of the bridge was performed in order to identify the relevant modal shapes in terms of period and participating mass. Results are summarized in Table 3 (the main mode is the 3rd, T = 0.53 s) and, in Figure 6, the modal deformed shapes of the deck (transversal direction) are plotted. The modes were selected following the indications of [34]; therefore, a lower bound of 3% for the participating mass was considered (modes having a lower value were neglected). The target cumulative participating mass was 90% and, considering mode 2, 3 and 4, the case study reached a value of 92.7%; the neglected modes were characterized by a participating mass lower than 1%. It is worth mentioning that for existing structures, modal characteristics can be retrieved using modal updating techniques [35]. Table 3. Modal analysis of the bridge: relevant modes in the transversal direction (mode 1, mode 3 and mode 4) having a participating mass ratio >3%.

Mode Period [sec] Participating Mass [%]
1 0.65 16.  The connection between the superstructure and the abutment is modeled as a rigid connection in the transversal direction. All the pier elements were modelled with nonlinear properties at the possible yield locations, i.e., plastic regions according to Eurocode 8. The plastic hinges were modelled with SAP2000 fiber (P-M2-M3) hinges. Unconfined concrete was assigned for the concrete cover and confined for the rest of the section; the Mander's [31] concrete model was used to define confined and unconfined concrete stress-strain relationships whereas the reinforcing steel parameters were assumed given the design parameters of B450C (Fy = 450 Mpa, Es = 210,000 Mpa, Fu = 540 Mpa).
The fiber hinges were defined by moment-rotation curves calculated using a fiber-based model of the cross-section according to the reinforcement details at the hinge locations. The constitutive model adopted for the concrete (both unconfined and confined) is the Mander's model and the rebar was considered consistently with the code parameters: fy = 450 Mpa, Es = 210,000 Mpa, fu = 540 Mpa. More complex models can be used to describe specific cyclic behavior of RC piers [32] also in the presence of corrosion [33].

Modal Properties
According to the IMPAb procedure, a modal analysis of the bridge was performed in order to identify the relevant modal shapes in terms of period and participating mass. Results are summarized in Table 3 (the main mode is the 3rd, T = 0.53 s) and, in Figure 6, the modal deformed shapes of the deck (transversal direction) are plotted. The modes were selected following the indications of [34]; therefore, a lower bound of 3% for the participating mass was considered (modes having a lower value were neglected). The target cumulative participating mass was 90% and, considering mode 2, 3 and 4, the case study reached a value of 92.7%; the neglected modes were characterized by a participating mass lower than 1%. It is worth mentioning that for existing structures, modal characteristics can be retrieved using modal updating techniques [35].

Nonlinear Analyses
The bridge was analyzed at several seismic intensity levels: considering a scale factor from 0.5 to 2.0 being the average PGA of the GM selected 0.32g and being PGA = 0.35 g the design value of the bridge analyzed.
The nonlinear dynamic analyses were preceded by the application of the gravity loads performing a nonlinear static analysis. The nonlinear response-history analysis (NRHA), performed using time increments of 0.1 s, was performed considering both the vertical and the horizontal component (transversal direction) of the ground motion. Among the common methods provided by SAP2000 software for conducting direct-integration time history analysis, the Hibler-Hughes-Taylor alpha (HHT) technique [36,37] was used in this study; the large displacement effects and material nonlinear properties were also considered. From Figures 7-9, the structural response to each GM is plotted in terms of deck displacement (transversal displacement of the deck at Pier 1, Pier 2 and Pier 3) and the variation of the axial load on each pier. The axial load variation is useful to evaluate the relevance of the vertical component of the GM in terms of axial load-bending moment interaction (the hinge of the piers are PM being P = axial load and M = bending moment) and therefore for the structural response; in a pushover analysis

Nonlinear Analyses
The bridge was analyzed at several seismic intensity levels: considering a scale factor from 0.5 to 2.0 being the average PGA of the GM selected 0.32g and being PGA = 0.35 g the design value of the bridge analyzed.
The nonlinear dynamic analyses were preceded by the application of the gravity loads performing a nonlinear static analysis. The nonlinear response-history analysis (NRHA), performed using time increments of 0.1 s, was performed considering both the vertical and the horizontal component (transversal direction) of the ground motion. Among the common methods provided by SAP2000 software for conducting direct-integration time history analysis, the Hibler-Hughes-Taylor alpha (HHT) technique [36,37] was used in this study; the large displacement effects and material nonlinear properties were also considered. From Figures 7-9, the structural response to each GM is plotted in terms of deck displacement (transversal displacement of the deck at Pier 1, Pier 2 and Pier 3) and the variation of the axial load on each pier. The axial load variation is useful to evaluate the relevance of the vertical component of the GM in terms of axial load-bending moment interaction (the hinge of the piers are PM being P = axial load and M = bending moment) and therefore for the structural response; in a pushover analysis this loading variation cannot be considered adopting procedures such as SPA, UPA or MPA. In all the cited pushover methods the analysis is performed starting from a preliminary nonlinear step in which the vertical static loads are imposed. As already discussed in the introduction, in a preliminary phase of this work, the use of EMPA (a modal pushover that includes also the vertical component of the seismic action) as an alternative to MPA was evaluated. This modification of the IMPAb was discarded because the results, using MPA or EMPA were very similar as discussed below. component (transversal direction) of the ground motion. Among the common methods provided by SAP2000 software for conducting direct-integration time history analysis, the Hibler-Hughes-Taylor alpha (HHT) technique [36,37] was used in this study; the large displacement effects and material nonlinear properties were also considered. From Figures 7-9, the structural response to each GM is plotted in terms of deck displacement (transversal displacement of the deck at Pier 1, Pier 2 and Pier 3) and the variation of the axial load on each pier. The axial load variation is useful to evaluate the relevance of the vertical component of the GM in terms of axial load-bending moment interaction (the hinge of the piers are PM being P = axial load and M = bending moment) and therefore for the structural response; in a pushover analysis this loading variation cannot be considered adopting procedures such as SPA, UPA or MPA. In all the cited pushover methods the analysis is performed starting from a preliminary nonlinear step in which the vertical static loads are imposed. As already discussed in the introduction, in a preliminary phase of this work, the use of EMPA (a modal pushover that includes also the vertical component of the seismic action) as an alternative to MPA was evaluated. This modification of the IMPAb was discarded because the results, using MPA or EMPA were very similar as discussed below.
AMT FEMA  As one can observe from Figures 7-9 (only the scale factor SF = 1.0 is plotted for the sake of brevity), the response to AMT record is characterized by the highest variation of the piers axial load (about ±40% of variation from the static load determined in seismic condition and used for the pushover analyses). This condition may suggest that the vertical action is relevant, and therefore, it can compromise results of a static pushover analysis. However this remark, that is true only for some typologies of structures and in particular only for some specific typologies of bridges (e.g., cable- As one can observe from Figures 7-9 (only the scale factor SF = 1.0 is plotted for the sake of brevity), the response to AMT record is characterized by the highest variation of the piers axial load (about ±40% of variation from the static load determined in seismic condition and used for the pushover analyses). This condition may suggest that the vertical action is relevant, and therefore, it can compromise results of a static pushover analysis. However this remark, that is true only for some typologies of structures and in particular only for some specific typologies of bridges (e.g., cable- As one can observe from Figures 7-9 (only the scale factor SF = 1.0 is plotted for the sake of brevity), the response to AMT record is characterized by the highest variation of the piers axial load (about ±40% of variation from the static load determined in seismic condition and used for the pushover analyses). This condition may suggest that the vertical action is relevant, and therefore, it can compromise results of a static pushover analysis. However this remark, that is true only for some typologies of structures and in particular only for some specific typologies of bridges (e.g., cable-stayed bridges [19]), cannot be applied to bridges, like the case study of this work, since the gravity loads influenced the design of the deck but not that of the pier. In fact, piers are usually designed with the bending action and ductility requirements (Eurocode 8 in this case [38]). Moreover, the axial load capacity is determined considering loading conditions (e.g., traffic load) that are much stronger than the seismic vertical action. The case study analyzed is an example of this condition; Figure 10 demonstrates that even a variation of axial load of about ±40% (that is the highest of the sets of time histories selected) does not influence the cross-section plastic behavior and therefore, the capacity of the piers. This condition encourages the development and testing of pushover-based procedures also for bridges under near-fault seismic events and it justifies the good performance of IMPAb described in ( §5).
Appl. Sci. 2020, 10, x FOR PEER REVIEW 12 of 19 stayed bridges [19]), cannot be applied to bridges, like the case study of this work, since the gravity loads influenced the design of the deck but not that of the pier. In fact, piers are usually designed with the bending action and ductility requirements (Eurocode 8 in this case [38]). Moreover, the axial load capacity is determined considering loading conditions (e.g., traffic load) that are much stronger than the seismic vertical action. The case study analyzed is an example of this condition; Figure 10 demonstrates that even a variation of axial load of about ±40% (that is the highest of the sets of time histories selected) does not influence the cross-section plastic behavior and therefore, the capacity of the piers. This condition encourages the development and testing of pushover-based procedures also for bridges under near-fault seismic events and it justifies the good performance of IMPAb described in ( §5). In Figures 11-13 are displayed the deformed shapes of the deck when the maximum displacement of the monitoring point (P1) has been recorded. From the analysis, it emerged that, in the near-field case the structural response was characterized by the contemporary achievement of the maximum displacement of the monitoring point and the maximum global base shear, which is different to what usually happens when performing NRHA with FF ground motions. By comparing Figures 11-13 and observing Figure 14 it is clear how the inelastic response, for scale factors greater than 1.0, modifies the response and the deformed shape changes becoming more uniform and less similar to a modal shape.  In Figures 11-13 are displayed the deformed shapes of the deck when the maximum displacement of the monitoring point (P1) has been recorded. From the analysis, it emerged that, in the near-field case the structural response was characterized by the contemporary achievement of the maximum displacement of the monitoring point and the maximum global base shear, which is different to what usually happens when performing NRHA with FF ground motions. By comparing Figures 11-13 and observing Figure 14 it is clear how the inelastic response, for scale factors greater than 1.0, modifies the response and the deformed shape changes becoming more uniform and less similar to a modal shape.
Appl. Sci. 2020, 10, x FOR PEER REVIEW 12 of 19 stayed bridges [19]), cannot be applied to bridges, like the case study of this work, since the gravity loads influenced the design of the deck but not that of the pier. In fact, piers are usually designed with the bending action and ductility requirements (Eurocode 8 in this case [38]). Moreover, the axial load capacity is determined considering loading conditions (e.g., traffic load) that are much stronger than the seismic vertical action. The case study analyzed is an example of this condition; Figure 10 demonstrates that even a variation of axial load of about ±40% (that is the highest of the sets of time histories selected) does not influence the cross-section plastic behavior and therefore, the capacity of the piers. This condition encourages the development and testing of pushover-based procedures also for bridges under near-fault seismic events and it justifies the good performance of IMPAb described in ( §5). In Figures 11-13 are displayed the deformed shapes of the deck when the maximum displacement of the monitoring point (P1) has been recorded. From the analysis, it emerged that, in the near-field case the structural response was characterized by the contemporary achievement of the maximum displacement of the monitoring point and the maximum global base shear, which is different to what usually happens when performing NRHA with FF ground motions. By comparing Figures 11-13 and observing Figure 14 it is clear how the inelastic response, for scale factors greater than 1.0, modifies the response and the deformed shape changes becoming more uniform and less similar to a modal shape.     Figure 15 illustrates that standard pushover methods, that adopt a first mode loading pattern (SPA) or a uniform loading pattern (UPA), differ (for high intensities, SF = 2.0) from the results of the nonlinear dynamic analysis both in terms of values and trend of the deformed shape. By enveloping the modal and the uniform pushover a better response evaluation can be derived; this envelope proposed in IMPAb is well performing if compared with NRHA for an intensity level corresponding to a scale factor 1.0 and therefore to a PGA = 0.32 g, which is very close to the bridge design intensity (PGA = 0.35 g). All the nonlinear static procedures considered underestimate the response at the center (P2) and at the flexible side (P3). This result is consistent to what was obtained in [18], applying IMPAb to the same case study for far-field events (FF).    Figure 15 illustrates that standard pushover methods, that adopt a first mode loading pattern (SPA) or a uniform loading pattern (UPA), differ (for high intensities, SF = 2.0) from the results of the nonlinear dynamic analysis both in terms of values and trend of the deformed shape. By enveloping the modal and the uniform pushover a better response evaluation can be derived; this envelope proposed in IMPAb is well performing if compared with NRHA for an intensity level corresponding to a scale factor 1.0 and therefore to a PGA = 0.32 g, which is very close to the bridge design intensity (PGA = 0.35 g). All the nonlinear static procedures considered underestimate the response at the center (P2) and at the flexible side (P3). This result is consistent to what was obtained in [18], applying IMPAb to the same case study for far-field events (FF).    Figure 15 illustrates that standard pushover methods, that adopt a first mode loading pattern (SPA) or a uniform loading pattern (UPA), differ (for high intensities, SF = 2.0) from the results of the nonlinear dynamic analysis both in terms of values and trend of the deformed shape. By enveloping the modal and the uniform pushover a better response evaluation can be derived; this envelope proposed in IMPAb is well performing if compared with NRHA for an intensity level corresponding to a scale factor 1.0 and therefore to a PGA = 0.32 g, which is very close to the bridge design intensity (PGA = 0.35 g). All the nonlinear static procedures considered underestimate the response at the center (P2) and at the flexible side (P3). This result is consistent to what was obtained in [18], applying IMPAb to the same case study for far-field events (FF).  Figure 15 illustrates that standard pushover methods, that adopt a first mode loading pattern (SPA) or a uniform loading pattern (UPA), differ (for high intensities, SF = 2.0) from the results of the nonlinear dynamic analysis both in terms of values and trend of the deformed shape. By enveloping the modal and the uniform pushover a better response evaluation can be derived; this envelope proposed in IMPAb is well performing if compared with NRHA for an intensity level corresponding to a scale factor 1.0 and therefore to a PGA = 0.32 g, which is very close to the bridge design intensity (PGA = 0.35 g). All the nonlinear static procedures considered underestimate the response at the center (P2) and at the flexible side (P3). This result is consistent to what was obtained in [18], applying IMPAb to the same case study for far-field events (FF). According to the results presented in other works considering FF events (Kappos et al. [35,36]), the application with NF events confirmed that for bridges having a main translational mode (mode 3) with nonsymmetric modal shapes (mode 1 and 4), it is crucial to first activate the plastic hinges as shown in Figure 16. The mode shape changed when the hinge occurred in P2 and, as it can be observed in Figures  15 and 16, the MPA cannot follow this relevant modification of the dynamic response of the bridge. The modal pushover analysis is well performing in the case of an earthquake with a PGA corresponding to the design value (PGA = 0.35 g, the hinge in P2 is active); this latter condition is related to the fact that the bridge response was conditioned by the superstructure. In Figure 17, the MPA-UPAenv curves are compared with results from nonlinear response history analysis, the modal According to the results presented in other works considering FF events (Kappos et al. [35,36]), the application with NF events confirmed that for bridges having a main translational mode (mode 3) with nonsymmetric modal shapes (mode 1 and 4), it is crucial to first activate the plastic hinges as shown in Figure 16. According to the results presented in other works considering FF events (Kappos et al. [35,36]), the application with NF events confirmed that for bridges having a main translational mode (mode 3) with nonsymmetric modal shapes (mode 1 and 4), it is crucial to first activate the plastic hinges as shown in Figure 16. The mode shape changed when the hinge occurred in P2 and, as it can be observed in Figures  15 and 16, the MPA cannot follow this relevant modification of the dynamic response of the bridge. The modal pushover analysis is well performing in the case of an earthquake with a PGA corresponding to the design value (PGA = 0.35 g, the hinge in P2 is active); this latter condition is related to the fact that the bridge response was conditioned by the superstructure. In Figure 17, the MPA-UPAenv curves are compared with results from nonlinear response history analysis, the modal The mode shape changed when the hinge occurred in P2 and, as it can be observed in Figures 15 and 16, the MPA cannot follow this relevant modification of the dynamic response of the bridge. The modal pushover analysis is well performing in the case of an earthquake with a PGA corresponding to the design value (PGA = 0.35 g, the hinge in P2 is active); this latter condition is related to the fact that the bridge response was conditioned by the superstructure. In Figure 17, the MPA-UPAenv curves are compared with results from nonlinear response history analysis, the modal pushover and the nonlinear dynamic response are quite similar up to the real average intensity of the seismic event (from PGA 0.16 g to PGA 0.32 g), but the envelope of modal and uniform pushover achieved a better estimation.
Appl. Sci. 2020, 10, x FOR PEER REVIEW 15 of 19 pushover and the nonlinear dynamic response are quite similar up to the real average intensity of the seismic event (from PGA 0.16 g to PGA 0.32 g), but the envelope of modal and uniform pushover achieved a better estimation. For higher intensities (scale factor 2.0: PGA = 0.64 g) a good estimation of displacement was only observed at Pier 1, according to the experience from FF events; from Figures 14 and 16, it can be observed that the first plastic hinges occurred, for an intensity level (about PGA = 0.3 g,) lower than the design one, first in P2 than in P1. The first hinge in P3 occurred at a very high intensity level (higher than PGA 0.64 g). The ultimate limit state at the base of P2 was achieved for a PGA = 0.5 g at P2; consequently the investigation of intensities greater 0.5 g is considered useless for the purpose of this procedure. Figures 17 and 18 illustrate the capacity curves obtained, within the intensity range adopted, with the incremental modal pushover (IMPA), incremental standard pushover (ISPA), incremental uniform pushover (IUPA) and with IMPAb and the incremental dynamic analysis (IDA). The comparison confirmed a very good accuracy for IMPAb also for NF events; the response obtained with IDA was, similarly to what was observed with FF and therefore the IMPAb can be considered the best method since it offers a good fit of the IDA curve, within the limits of the case study.  For higher intensities (scale factor 2.0: PGA = 0.64 g) a good estimation of displacement was only observed at Pier 1, according to the experience from FF events; from Figures 14 and 16, it can be observed that the first plastic hinges occurred, for an intensity level (about PGA = 0.3 g), lower than the design one, first in P2 than in P1. The first hinge in P3 occurred at a very high intensity level (higher than PGA 0.64 g). The ultimate limit state at the base of P2 was achieved for a PGA = 0.5 g at P2; consequently the investigation of intensities greater 0.5 g is considered useless for the purpose of this procedure. Figures 17 and 18 illustrate the capacity curves obtained, within the intensity range adopted, with the incremental modal pushover (IMPA), incremental standard pushover (ISPA), incremental uniform pushover (IUPA) and with IMPAb and the incremental dynamic analysis (IDA). The comparison confirmed a very good accuracy for IMPAb also for NF events; the response obtained with IDA was, similarly to what was observed with FF and therefore the IMPAb can be considered the best method since it offers a good fit of the IDA curve, within the limits of the case study.

Conclusions
Appl. Sci. 2020, 10, x FOR PEER REVIEW 15 of 19 pushover and the nonlinear dynamic response are quite similar up to the real average intensity of the seismic event (from PGA 0.16 g to PGA 0.32 g), but the envelope of modal and uniform pushover achieved a better estimation. For higher intensities (scale factor 2.0: PGA = 0.64 g) a good estimation of displacement was only observed at Pier 1, according to the experience from FF events; from Figures 14 and 16, it can be observed that the first plastic hinges occurred, for an intensity level (about PGA = 0.3 g,) lower than the design one, first in P2 than in P1. The first hinge in P3 occurred at a very high intensity level (higher than PGA 0.64 g). The ultimate limit state at the base of P2 was achieved for a PGA = 0.5 g at P2; consequently the investigation of intensities greater 0.5 g is considered useless for the purpose of this procedure. Figures 17 and 18 illustrate the capacity curves obtained, within the intensity range adopted, with the incremental modal pushover (IMPA), incremental standard pushover (ISPA), incremental uniform pushover (IUPA) and with IMPAb and the incremental dynamic analysis (IDA). The comparison confirmed a very good accuracy for IMPAb also for NF events; the response obtained with IDA was, similarly to what was observed with FF and therefore the IMPAb can be considered the best method since it offers a good fit of the IDA curve, within the limits of the case study.

Conclusions
This work has presented a study finalized to develop a pushover-based procedure to perform a comprehensive assessment of the behavior of bridges under near-fault seismic loads. This innovative procedure, named IMPAb, is alternative to what is currently considered the most reliable procedure, the incremental dynamic analysis (IDA), and its reliability has been demonstrated through the application to an irregular bridge.
This study follows previous experiences of the same authors developing a nonlinear static procedure for buildings and bridges. The primary objective of this paper was to verify the validity of results of the IMPAb (incremental procedure for bridges) subjected to near-fault ground motions. The procedure requires nonlinear static analyses to estimate the seismic demands for bridge structures. In a previous study, IMPAb was developed specifically for bridges and it was tested with far-field events only, proving its effectivity for the same irregular bridge.
The procedure, summarized in Figure 19, requires the following main steps: (1) Definition of the seismic capacity of the bridge performing two different pushover procedures: the modal pushover (MPA) and a pushover with uniform load pattern (UPA); (2) Definition of the seismic demand in terms of response spectrum; (3) Selection of a performance point with both the pushover approaches within a predefined range of intensities (the modal pushover requires to combine results from any pushover performed required (step 2a); (4) Evaluation of the structural response in terms of deck displacement and base shear or in terms of deck displacement (using this parameter as a damage index) and seismic intensity. The deck displacement is described selecting a representative joint (the monitoring point). This work has presented a study finalized to develop a pushover-based procedure to perform a comprehensive assessment of the behavior of bridges under near-fault seismic loads. This innovative procedure, named IMPAb, is alternative to what is currently considered the most reliable procedure, the incremental dynamic analysis (IDA), and its reliability has been demonstrated through the application to an irregular bridge.
This study follows previous experiences of the same authors developing a nonlinear static procedure for buildings and bridges. The primary objective of this paper was to verify the validity of results of the IMPAb (incremental procedure for bridges) subjected to near-fault ground motions. The procedure requires nonlinear static analyses to estimate the seismic demands for bridge structures. In a previous study, IMPAb was developed specifically for bridges and it was tested with far-field events only, proving its effectivity for the same irregular bridge.
The procedure, summarized in Figure 19, requires the following main steps: (1) Definition of the seismic capacity of the bridge performing two different pushover procedures: the modal pushover (MPA) and a pushover with uniform load pattern (UPA); Definition of the seismic demand in terms of response spectrum; (2) Selection of a performance point with both the pushover approaches within a predefined range of intensities (the modal pushover requires to combine results from any pushover performed required (step 2a); (3) Evaluation of the structural response in terms of deck displacement and base shear or in terms of deck displacement (using this parameter as a damage index) and seismic intensity. The deck displacement is described selecting a representative joint (the monitoring point). The influence of different load patterns, including the solution proposed in IMPAb, on different seismic demands (deck displacement, capacity curve) was investigated in this paper. The following conclusions can be drawn from this study that is limited to a single case study and, therefore, will be followed by a more extended validation. The influence of different load patterns, including the solution proposed in IMPAb, on different seismic demands (deck displacement, capacity curve) was investigated in this paper. The following conclusions can be drawn from this study that is limited to a single case study and, therefore, will be followed by a more extended validation.
The application presented shows that in case of pulse-like near-fault seismic events the use of MPA is equivalent to the use of EMPA (that is a modal pushover performed including the vertical seismic action). According to what was already observed also for far-field events, the response evaluated with MPA, UPA (or even SPA) presents some differences. In particular, considering NF events and comparing pushover and NRHA, the following considerations emerges: • MPA overestimates the response at P1 and underestimates the response at P2 and P3 ( Figure 5). • UPA underestimates the response at P1 while at P2 and P3, gives results very similar to NRHA. • Performing IMPAb, according to the procedure originally defined (enveloping UPA and MPA) the obtained response is very similar to IDA, according to what was already observed considering FF events.
Therefore, this new application of the procedure IMPAb shows a satisfactory estimation of the structural response of a bridge under near-field events in terms of deck displacement for intensities up to the achievement of the first collapse (ultimate curvature achieved in a pier plastic hinge). Good results were obtained in terms of definition of the capacity curve both considering the maximum values of the displacement Vs base shear or the monitoring point displacement Vs seismic intensity. Therefore, the proposed procedure, which has been proved accurate for the response to near-fault pulse like seismic events as well, can give a valid contribution in the field of bridge seismic assessment. IMPAb is a valid nonlinear static procedure alternative to nonlinear dynamic-based methods.

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