Report - PEER - University of California, Berkeley
Report - PEER - University of California, Berkeley Report - PEER - University of California, Berkeley
Dutta and Das (2002, 2002b and refs. therein) also used one-storey models tostudy the effect of strength deterioration on the bidirectional response of codedesignedasymmetric structures. They concluded that the displacement and ductilitydemands on the flexible edge as well as on the rigid edge were much larger than thoseof their symmetric counterparts and of similar models but without strengthdeterioration. They also observed that the unidirectional input might grosslyunderestimate the response. These issues deserve further study.Stathopoulos and Anagnostopoulos (2003) examined critically the use of 1-storeymodels as proxies for multistorey asymmetric frame structures. These are due to theassumption that plastic hinges form in columns, rather than in beams. For examplethey found that the simple 1-mass shear-spring (or shear-beam) models commonlyused by researchers to assess seismic provisions may not be appropriate, since suchmodels over-predict the flexible edge displacements, as noted earlier by Ghersi et al.(1999).The easier accessibility of nonlinear 3-D computer programs in the 1990s freedresearchers from the need to extrapolate from the 1-storey models. Yet, single masstorsional behaviour continues to attract many researchers, mainly because it is able toprovide qualitative information on the global behaviour at low computational effort,and even to reveal hitherto unknown phenomena. Indeed, the second part of this paperpresents a design procedure based on single mass response.Most of the interest focused on multistorey frame structures, while severalstudies on wall-frames were also reported, and will be referred to subsequently.Studies by Duan and Chandler (1993) on multistorey structures modelled as shearbeams showed that there could be problems with uncritical extrapolation of 1-storeyresults. Nassar and Krawinkler (1991) observed that such modelling is likely to beconservative because realistic cases, in which plastic hinges form at beam-ends,usually show smaller ductility demands. Moghadam and Tso (1996) observed thatshear beam modelling does not lead to reliable estimates of important designparameters. They also concluded that the seismic provisions could not adequatelyprotect torsionally flexible buildings.De Stefano et al. (2002) studied the response of a code-designed unidirectionallyexcited 6-storey frame building. They attributed the excessive ductility demands inunexpected locations to overstrength, and concluded that code-designs, which arecalibrated to 1-storey models, may not achieve their goal of bringing the ductilitydemands in asymmetric structures in line with their symmetric counterparts. Thismatter should be further explored.Reports on multistorey asymmetric structures under bi-directional excitation alsobegan to emerge in the late 1990s, along with studies on unidirectionally excitedstructures. Fajfar and coworkers (e.g., Marusic and Fajfar 1999) compared theresponse of mass eccentric perimeter frame 5-storey models with their torsionallyflexible counterparts, i.e., those with lateral load resisting internal frames. Theydemonstrated that, as in 1-storey frames, increasing the ground motion intensitylowers twist amplification of the torsionally flexible structures. They also suggested371
that the SRSS combination of the two separate orthogonal inputs is a conservativeestimate of the response. More recently Rutenberg et al. (2002) demonstrated the hightorsional stiffness and strength of perimeter frame structures on the SAC 9-storeybuildings modelled as mass eccentric structures and excited bidirectionally. They alsoconcluded that corner columns could be quite vulnerable, as noted earlier by, e.g.,Cruz and Cominetti (2000). The recent study of Stathopoulos and Anagnostopoulos(2002) on 3 and 5 storey frame structures designed per EC8 concluded that even morecaution should be exercised when extrapolating from one-storey models. Forexample, they found that whereas in some cases code-designs lead to large ductilitydemands on the stiff side elements, the opposite results were obtained for thecorresponding multistorey structure. They also concluded that the amplification ofeccentricity as required by SEAOC/UBC has relatively small effect on the response,and hence does not appear to justify the additional computational effort involved.Finally, they found, as also some other researchers did, that code-design did notadequately protect the flexible edge elements. Very recently De la Colina (2003)presented a parameter study on code-designed 5-storey eccentric stiffness shearbuildings excited by the two components of the 1940 El Centro record. The resultsconfirm those obtained from 1-storey models, namely that a design eccentricity of1.5e for elements located on the flexible side of the floor deck and of 0.5e for therigid side elements recommended by several seismic codes lead to ductility demandslower or equal to those obtained for similar elements in similar but torsionallybalanced systems. He also concluded that an eccentricity not lesser than 0.2e forstoreys with very small or zero eccentricity should be stipulated in order to avoidexcessive ductility demand, again in line with some codes.The application of pushover analysis to asymmetric structures has becomepopular since the mid 1990s. However, assigning a shape to the loading vector is amuch more difficult problem than for the corresponding 2-D problem, (while thechoice of the target displacement is probably not). Several approaches have beenproposed. The simplest one is to apply the code loading shape along the mass axis ofthe building, or at a prescribed offset (the design eccentricity) until the targetdisplacement is reached. Indeed many earlier studies took this approach (seeRutenberg 2002). More recent studies by Fajfar and coworkers (e.g., Fajfar et al.2002) extended the N2 method to bidirectionally excited multistorey structures byevaluating the performance point separately for each direction and then combining theresults by means of the SRSS formula. Again, they concluded that for torsionally stiffstructures the approach leads to acceptable results. Ayala and Tavera (2002) proposea pushover procedure in which the shapes of the lateral loads in the two orthogonaldirections and of the torques about CM are obtained from 3-D modal analysis usingaccepted modal combination rules. The resulting 2 base shear and the base torqueversus roof displacement/rotation curves are converted into the 1st mode behaviourcurves and further transformed into the 1-DOF behaviour curve. Good prediction ofthe response is shown for the example 8-storey frame building. Chopra and Goel(2003) extended their modal pushover analysis procedure to asymmetric structures.372
- Page 336 and 337: ON DRIFT LIMITS ASSOCIATED WITH DIF
- Page 338 and 339: BehaviourElasticInelasticCollapseDa
- Page 340 and 341: Other factors such as the applied l
- Page 342 and 343: 4. MOMENT RESISTING FRAMES4.1 Ducti
- Page 344 and 345: 5Ductility factor432100 0.2 0.4 0.6
- Page 346 and 347: 5.1 Flexural Structural WallsAn exa
- Page 348 and 349: MODAL PUSHOVER ANALYSIS: SYMMETRIC-
- Page 350 and 351: Floor963SeattleNonlinear RHAFEMA1st
- Page 352 and 353: The peak modal demands r n are then
- Page 354 and 355: 9BostonSeattleLos AngelesFloor63RSA
- Page 356 and 357: 5. EVALUATION OF MPA: UNSYMMETRIC-P
- Page 358 and 359: Without additional conceptual compl
- Page 360 and 361: AN IMPROVED PUSHOVER PROCEDURE FOR
- Page 362 and 363: for a response governed by the fund
- Page 364 and 365: 2.2 Modal ScalingThe principal aim
- Page 366 and 367: 2.3 Pushover-History AnalysisSubsti
- Page 368 and 369: (3) Calculate cumulative scale fact
- Page 370 and 371: 46.4 58 58 58 58 58 58 58 58 58 58
- Page 372 and 373: EXTENSIONS OF THE N2 METHOD — ASY
- Page 374 and 375: The strength reduction factor due t
- Page 376 and 377: The relations apply to SDOF systems
- Page 378 and 379: in X-direction pushover curves prac
- Page 380 and 381: As an example, an idealized force-d
- Page 382 and 383: The IN2 curve can be used in the pr
- Page 384 and 385: HORIZONTALLY IRREGULAR STRUCTURES:
- Page 388 and 389: They tested the procedure on three
- Page 390 and 391: Table 1. Properties of the 4 WallsW
- Page 392 and 393: The following is a summary of two s
- Page 394 and 395: ectangular concrete deck supported
- Page 396 and 397: REFERENCESAlmazan, J. L., and J. C.
- Page 398 and 399: Rosenblueth, E. (1957). “Consider
- Page 400 and 401: instantaneous period of vibration a
- Page 402 and 403: value of the maximum plastic deform
- Page 404 and 405: (a) elastic-perfectly plastic type(
- Page 406 and 407: where a is the constant peculiar to
- Page 408 and 409: Referring to Eq. (15), the natural
- Page 410 and 411: -The effective period obtained by u
- Page 412 and 413: eal damage data, rather than theore
- Page 414 and 415: liquefaction-induced damage. This i
- Page 416 and 417: Figure 5. Selected damage distribut
- Page 418 and 419: Figure 6. Idealized capacity spectr
- Page 420 and 421: I’ for the ductile case, as expec
- Page 422 and 423: This study has shown that a modific
- Page 424 and 425: thickness of the inner wall is usua
- Page 426 and 427: 4. EARTHQUAKE GROUND MOTION INPUT A
- Page 428 and 429: 5.2 Performance Levels and Limit St
- Page 430 and 431: where λ I jis the occurrence rate
- Page 432 and 433: intensity VI because the number of
- Page 434 and 435: and thus are not considered in seis
that the SRSS combination <strong>of</strong> the two separate orthogonal inputs is a conservativeestimate <strong>of</strong> the response. More recently Rutenberg et al. (2002) demonstrated the hightorsional stiffness and strength <strong>of</strong> perimeter frame structures on the SAC 9-storeybuildings modelled as mass eccentric structures and excited bidirectionally. They alsoconcluded that corner columns could be quite vulnerable, as noted earlier by, e.g.,Cruz and Cominetti (2000). The recent study <strong>of</strong> Stathopoulos and Anagnostopoulos(2002) on 3 and 5 storey frame structures designed per EC8 concluded that even morecaution should be exercised when extrapolating from one-storey models. Forexample, they found that whereas in some cases code-designs lead to large ductilitydemands on the stiff side elements, the opposite results were obtained for thecorresponding multistorey structure. They also concluded that the amplification <strong>of</strong>eccentricity as required by SEAOC/UBC has relatively small effect on the response,and hence does not appear to justify the additional computational effort involved.Finally, they found, as also some other researchers did, that code-design did notadequately protect the flexible edge elements. Very recently De la Colina (2003)presented a parameter study on code-designed 5-storey eccentric stiffness shearbuildings excited by the two components <strong>of</strong> the 1940 El Centro record. The resultsconfirm those obtained from 1-storey models, namely that a design eccentricity <strong>of</strong>1.5e for elements located on the flexible side <strong>of</strong> the floor deck and <strong>of</strong> 0.5e for therigid side elements recommended by several seismic codes lead to ductility demandslower or equal to those obtained for similar elements in similar but torsionallybalanced systems. He also concluded that an eccentricity not lesser than 0.2e forstoreys with very small or zero eccentricity should be stipulated in order to avoidexcessive ductility demand, again in line with some codes.The application <strong>of</strong> pushover analysis to asymmetric structures has becomepopular since the mid 1990s. However, assigning a shape to the loading vector is amuch more difficult problem than for the corresponding 2-D problem, (while thechoice <strong>of</strong> the target displacement is probably not). Several approaches have beenproposed. The simplest one is to apply the code loading shape along the mass axis <strong>of</strong>the building, or at a prescribed <strong>of</strong>fset (the design eccentricity) until the targetdisplacement is reached. Indeed many earlier studies took this approach (seeRutenberg 2002). More recent studies by Fajfar and coworkers (e.g., Fajfar et al.2002) extended the N2 method to bidirectionally excited multistorey structures byevaluating the performance point separately for each direction and then combining theresults by means <strong>of</strong> the SRSS formula. Again, they concluded that for torsionally stiffstructures the approach leads to acceptable results. Ayala and Tavera (2002) proposea pushover procedure in which the shapes <strong>of</strong> the lateral loads in the two orthogonaldirections and <strong>of</strong> the torques about CM are obtained from 3-D modal analysis usingaccepted modal combination rules. The resulting 2 base shear and the base torqueversus ro<strong>of</strong> displacement/rotation curves are converted into the 1st mode behaviourcurves and further transformed into the 1-DOF behaviour curve. Good prediction <strong>of</strong>the response is shown for the example 8-storey frame building. Chopra and Goel(2003) extended their modal pushover analysis procedure to asymmetric structures.372