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The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 1
PERFORMANCE OF A NONDUCTILE RC BUILDING FOR THE FEMA P695 FAR-FAULT
GROUND MOTION DATA SET
Adolfo B. Matamoros, Anil Suwal, and Andres Lepage
Fall 2018 ACI ConventionOctober 13-17, 2018Las Vegas, Nevada
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 2
Rehabilitation ObjectiveModeling Parameters Acceptance Criteria
Maximum Cons ideredEarthquake
474 yrs
225 yrs
72 yrs
2475 yrs
ASCE-41 Standard
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 3
FEMA P695 Methodology
Equivalent safety against collapse for buildings with different seismic force resisting systems
Collapse Safety Margin
Global InstabilityLocal Instability
Median Collapse: One-half of the structures have some form of collapse
Collapse Margin Ratio, CMR =SA Median collapse-level ground motions
SA of MCE ground motions
NEHRP: Structure should have a low probability of collapse for MCE (1.5 times the design level earthquake)
Design Criteria for Building Codes (i.e. R, Cd, and Ω0 seismic performance factors)
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 4
Building Description• Seven-story RC Building in Van Nuys, CA• Designed in 1965 and constructed in 1966• Exterior moment-resisting frames• Interior gravity load flat slab system• Strong motion records from:
– 1971 San Fernando – 1987 Whittier – 1990 Upland– 1992 Sierra Madre– 1994 Northridge
• Light structural damage during the 1971 San Fernando Earthquake, severe column damage during the 1995 Northridge earthquake.
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 5
Building Plan
40 x 56 cm spandrel beam around perimeter (40 x75 cm first floor)
35 x 50 cmext. columns
45 cm square int. columns
19.1 m
45.7 m
interior frame
exterior frame
N
S
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 6
Lumped Plasticity Model for Frame Structure
Moment rotation relationship for nonlinear rotational spring of second story column of RC Building
Rotation
Mo
men
t
Two Node Joint Elastic ElementJoint Offset
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 7
Collapse Simulation
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 8
CMR is established through Incremental Dynamic Analysis
-200
-100
0
100
200
0 5 10 15 20
Ground motion set scaled to MCE
Ground motion records
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 9
Collapse Simulation Results EW Direction
0
500
1000
1500
2000
2500
0 0.02 0.04 0.06 0.08
Mom
ent
(kip
in.)
Rotation (radians)
ASCE 41-13 column ACI 369 column
0.0
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
1.0
0.0 0.3 0.5 0.8 1.0 1.3 1.5 1.8 2.0 2.3 2.5
Pro
babil
ity o
f C
oll
apse
due t
o
Late
ral In
stabilit
y
Intensity Measure (IM)
ASCE 41 Model
ACI 369 ModelNorthridge
50% PE
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 10
Two Node Joint Elastic ElementJoint Offset
ASCE 41-13 ASCE 41-17
Probability of
Exceeding Column
Modeling Parameters
Northridge
50% PE
Northridge
50% PE
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 11
Two Node Joint Elastic ElementJoint Offset
ASCE 41-13 ASCE 41-17
Probability of
Exceeding Column
Acceptance Criteria
Northridge
50% PE
Northridge
50% PE
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 12
Fragility Relationships for AC in ASCE 41-13 and ASCE 41-17
Columns Beams
17
13
13
17
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 13
Backbone curve parameters
• Yield strength – Fy
• Initial or Elastic stiffness – Ke
• Strain-Hardening stiffness – Ks
• Post-Capping stiffness – Kc
• Residual strength Fr
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 14
ACI 369 Section 3.1.2.2 Nonlinear Procedures
Point C shall have an ordinate equal to the strength of the component and an abscissa equal to the deformation at which significant strength degradation begins.
anl
bnl
cnl
A
B
C
D E
QQy
1.0
dnl
enl
cnl
A
B
C
D E
QQy
1.0
Θ or Δ
Θ or Δ
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 15
0.0
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
1.0
0 1 2 3 4 5 6 7 8 9
ASCE 41 Comp
16 to 40%
ASCE 41 Non Compliant
Drift ratio at loss of lateral strength
5 to 27%
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 16
Effective stiffness coefficient for descending branch αd
ASCE 41-17 ModelCompliant low shear 32McCompliant high shear 40Mc
Non-compliant low shear 80McNon-compliant high shear 160Mc
PARAMETERS FROM STATISTICAL ANALYSISTest Data 25Mc
anl
bnl
cnl
A
B
C
D E
QQy
1.0
dnl
enl
cnl
A
B
C
D E
QQy
1.0
Θ or Δ
Θ or Δ
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 17
Conclusions
• Due to the lack of ductile detailing, the case-study building will reach local collapse at much lower earthquake intensities (50% at IM 0.65) than would cause dynamic instabilities (50% at IM 0.85).
• Comparison of fragility relationships based on ASCE 41-13 and -17 standards show that acceptance criteria for IO were similar, and that changes in acceptance criteria were noticeable for the LS and CP limit states.
• The greater gap between the curves corresponding to LS and CP observed for the ACI 369 acceptance criteria is a better representation of performance objectives defined in Chapter 2 of ASCE 41 where, for example, the Enhanced Objective corresponds both to seismic hazard level BSE-1 (10% probability of exceedance in 50 yrs) with performance level LS and seismic hazard level BSE-2 (2% probability of exceedance in 50 years) with performance objective CP.
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 18
Conclusions
• The performance level of the case study building was controlled by the exterior beams, which are the elements of least concern to the gravity load system. The effect of element damage on the probability of collapse should be considered when formulating Acceptance Criteria.
• Comparisons between models with ASCE 41-13 MP and AC and ASCE 41-17 MP and AC show that that the difference in MP of columns between the two provisions led to significant changes in the distribution of nonlinear deformation in the components of the system
• Analysis results show that plastic rotation demands in columns were much lower than plastic rotation demands in beams. This is attributed to the fact that in the 2017 provisions columns can reach deformations at loss of lateral load capacity as high as twice than those of beams
• It is very important to simulate system behavior accurately that MP and AC for beams and slab column connections be adjusted to have similar probabilities of exceedance than columns.
The University of Texas at San Antonio, One UTSA Circle, San Antonio, TX 782491/3/11 19
Acknowledgments
The authors would like to acknowledge the support of the National Science Foundation under award number 0618804 through the Pacific Earthquake Engineering Research Center (PEER).