DISPLACEMENT-BASED SEISMIC DESIGN
DISPLACEMENT-BASED SEISMIC DESIGN
DISPLACEMENT-BASED SEISMIC DESIGN
You also want an ePaper? Increase the reach of your titles
YUMPU automatically turns print PDFs into web optimized ePapers that Google loves.
ISRAELI STRUCTURAL ENGINEERING CONFERENCE<br />
TEL AVIV, JUNE 2009<br />
<strong>DISPLACEMENT</strong>-<strong>BASED</strong> <strong>SEISMIC</strong><br />
<strong>DESIGN</strong><br />
Nigel Priestley<br />
European School for Advanced Studies in<br />
Reduction of Seismic Risk, Pavia, Italy<br />
1
Review of a 15 year research effort<br />
culminating in the preparation of a design text<br />
book:<br />
<strong>DISPLACEMENT</strong>-<strong>BASED</strong> <strong>SEISMIC</strong><br />
<strong>DESIGN</strong> OF STRUCTURES<br />
Priestley, Calvi and Kowalsky<br />
IUSS Press (May 2007)<br />
Available online (www.iusspress.it)<br />
2
WITHIN A PERFORMANCE-<strong>BASED</strong><br />
ENVIRONMENT:<br />
• WHAT SHOULD BE THE STRUCTURAL<br />
STRENGTH (BASE SHEAR FORCE)<br />
• HOW SHOULD THIS STRENGTH BE<br />
DISTRIBUTED<br />
• HOW CAN <strong>DESIGN</strong> BE ELEVATED<br />
ABOVE ANALYSIS<br />
• WHAT SHOULD BE THE STRENGTH<br />
OF CAPACITY-PROTECTED ACTIONS<br />
3
1. The Need for DDBD<br />
(Problems with Force-based Design)<br />
• Estimating Elastic Stiffness<br />
• Distribution of Required Strength based on Elastic<br />
Stiffness<br />
• Displacement-Equivalence Rules (equal displacement)<br />
• Specified Ductility or Force-Reduction Factors<br />
• Assumption that Increased Strength Reduces<br />
potential for damage<br />
Note: Damage is strain or drift (not strength)<br />
related<br />
4
Concrete Bridge under Longitudinal Seismic Excitation<br />
Spectral Acceleration S A(T)<br />
H A H<br />
H C<br />
B<br />
C<br />
A<br />
B<br />
Structure<br />
Elastic<br />
Ductile<br />
Period T (seconds)<br />
Acceleration Response Spectrum<br />
K<br />
long<br />
Stiffness:<br />
= K + K<br />
A<br />
Period:<br />
T = 2π m /<br />
F<br />
i<br />
B<br />
+<br />
K long<br />
K<br />
C<br />
=<br />
Base shear force:<br />
=<br />
F =<br />
m ⋅<br />
g ⋅ S<br />
R<br />
A ( T )<br />
Pier Shear Force:<br />
F<br />
K<br />
K<br />
i<br />
long<br />
Design Displacement:<br />
2<br />
T<br />
∆<br />
long<br />
= ⋅ S<br />
2 A(<br />
T )<br />
4π<br />
⋅ g<br />
∑<br />
A,<br />
B,<br />
C<br />
5<br />
12EI<br />
H<br />
3
T = 2π m /<br />
K long<br />
Concrete Bridge Under Longitudinal Response<br />
H A H B<br />
H C<br />
C<br />
A<br />
Stiffness:<br />
K<br />
long<br />
B<br />
= K<br />
A<br />
+<br />
K<br />
B<br />
+<br />
K<br />
C<br />
=<br />
∑<br />
A,<br />
B,<br />
C<br />
12EI<br />
H<br />
3<br />
Period:<br />
T = 2π m /<br />
K long<br />
Pier Strength:<br />
F =<br />
i<br />
F<br />
K<br />
K<br />
i<br />
long<br />
What value for EI What force-reduction<br />
factor Is the strength distribution logical<br />
6
STIFFNESS OF CONCRETE ELEMENTS:<br />
Stiffness is assumed to be independent of strength,<br />
and a fixed percentage (often 100% or 50%) of gross<br />
(uncracked) section stiffness<br />
7
Elastic Stiffness<br />
40000<br />
EI=M y /φ y<br />
50000<br />
40000<br />
Nu/f'cAg = 0.4<br />
Nu/f'cAg = 0.3<br />
Nu/f'cAg = 0.2<br />
Nu/f'cAg = 0.1<br />
Moment (kNm)<br />
30000<br />
20000<br />
Nu/f'cAg = 0.4<br />
Nu/f'cAg = 0.3<br />
Nu/f'cAg = 0.2<br />
Nu/f'cAg = 0.1<br />
Nu/f'cAg = 0<br />
Moment (kNm)<br />
30000<br />
20000<br />
Nu/f'cAg = 0<br />
10000<br />
10000<br />
0<br />
0<br />
0 0.002 0.004 0.006<br />
Curvature (1/m)<br />
(a) Reinforcement Ratio = 1%<br />
0 0.002 0.004 0.006<br />
Curvature (1/m)<br />
(b) Reinforcement Ratio = 3%<br />
SELECTED MOMENT-CURVATURE CURVES FOR<br />
CIRCULAR COLUMNS (D=2m,f’ c = 35MPa, f y = 450MPa)<br />
8
Dimensionless Moment (M N<br />
/f'cD 3 )<br />
0.2<br />
0.16<br />
0.12<br />
0.08<br />
0.04<br />
0<br />
ρ l<br />
= 0.04<br />
ρ l<br />
= 0.03<br />
ρ l<br />
= 0.02<br />
ρ l<br />
= 0.01<br />
ρ l = 0.005<br />
Dimensionless Curvature (φ y<br />
D/ε y<br />
)<br />
2.5<br />
2<br />
1.5<br />
1<br />
0.5<br />
0<br />
Ave. +10%<br />
ρ l<br />
= 0.04<br />
Ave. -10%<br />
ρ l<br />
= 0.005<br />
Average φ y<br />
D/ε y<br />
= 2.25<br />
Average φ y<br />
D/ε y<br />
= 2.25<br />
0 0.1 0.2 0.3 0.4<br />
0 0.1 0.2 0.3 0.4<br />
Axial Load Ratio (N u<br />
/f'cA g<br />
)<br />
Axial Load Ratio (N u<br />
/f' c<br />
A g<br />
)<br />
(a) Nominal Moment<br />
(b) Yield Curvature<br />
DIMENSIONLESS NOMINAL MOMENT AND YIELD<br />
CURVATURE FOR CIRCULAR COLUMNS<br />
STRENGTH VARIES; YIELD CURVATURE IS CONSTANT<br />
9
1<br />
0.90<br />
0.8<br />
ρ l<br />
= 0.04<br />
Stiffness Ratio (EI/EI gross<br />
)<br />
0.6<br />
0.4<br />
ρ l<br />
= 0.03<br />
ρ l<br />
= 0.02<br />
ρ l<br />
= 0.01<br />
ρ l<br />
= 0.005<br />
EI eff = M N /φ y<br />
EI eff /EI gross<br />
=M N /φ y EI gross<br />
0.2<br />
0<br />
0.12<br />
0 0.1 0.2 0.3 0.4<br />
Axial Load Ratio (N u<br />
/f' c<br />
A g<br />
)<br />
EFFECTIVE STIFFNESS RATIO FOR<br />
CIRCULAR COLUMNS<br />
10
INTERDEPENDENCY OF STRENGTH AND STIFFNESS<br />
Stiffness EI = M/φ<br />
M<br />
M 1<br />
M<br />
M 1<br />
M 2<br />
M 2<br />
M 3<br />
M 3<br />
φ y3<br />
φ y2<br />
φ y1<br />
φ φ y<br />
φ<br />
(a) Design assumption<br />
(constant stiffness)<br />
(b) Realistic assumption<br />
(constant yield curvature)<br />
INFLUENCE OF STRENGTH ON MOMENT-CURVATURE RESPONSE<br />
11
Bridge Under Longitudinal Response: Elastic Strength<br />
Distribution<br />
Force-Based Design: Column Stiffness<br />
Force-Based Design: Column Moments:<br />
K = C EI<br />
i<br />
M = C V h =<br />
Bi<br />
h<br />
3<br />
1 i.<br />
eff<br />
/<br />
i<br />
C C<br />
EI<br />
h<br />
2<br />
2 i i 1 2 i.<br />
eff<br />
/<br />
i<br />
Short columns need highest long.rebar: stiffness increases: higher moment! 12
BRIDGE WITH UNEQUAL COLUMN HEIGHTS<br />
• Shortest piers are stiffest. Shear is in proportion to 1/h 3 .<br />
Therefore moments (and, approximately reinforcement ratio)<br />
are in proportion to 1/h 2 . Increasing the reinforcement ratio<br />
of the short piers relative to the long piers increases the<br />
relative stiffness of the short piers, attracting still higher<br />
shear in elastic response.<br />
• Allocating high shear to the short column increases its<br />
susceptibility to shear failure.<br />
• Displacement capacity of the short pier is DECREASED by<br />
increasing its reinforcement ratio<br />
• It doesn’t make sense to have a higher reinforcement ratio for<br />
the shorter columns than the longest columns (and in practice,<br />
they would probably have the same reinforcement ratio, for<br />
simplicity of construction)<br />
13
YIELD DRIFTS OF<br />
CONCRETE FRAMES<br />
ELASTIC DEFORMATION<br />
CONTRIBUTIONS TO DRIFT<br />
OF A BEAM/COLUMN<br />
JOINT SUBASSEMBLAGE<br />
Beam flexure and shear deform.<br />
Column flexure and shear deform.<br />
Joint shear deformation<br />
14
CONCRETE FRAME DRIFT EQUATION<br />
θ y = 0.5ε y (l b /h b )<br />
Equation Checked against test data with:<br />
• Column height/beam length aspect ratio (l c /l b ) : 0.4 – 0.86<br />
• Concrete compression strength (f’ c ) : 22.5MPa – 88MPa<br />
• Beam Reinforcement yield strength (f y ) : 276MPa – 611MPa<br />
• Maximum beam reinforcement ratio (A’ s /b w d) : 0.53% – 3.9%<br />
• Column axial load ratio (N u /f’ c A g ) : 0 – 0.483<br />
• Beam aspect ratio (l b /h b ) : 5.4 – 12.6<br />
15
θ y = 0.5ε y (l b /h b )<br />
EXPERIMENTAL DRIFTS OF BEAM/COLUMN<br />
TEST UNITS COMPARED WITH EQUATION<br />
16
DIMENSIONLESS YIELD CURVATURES<br />
AND DRIFTS<br />
• Circular column: φ = 2.25ε<br />
D<br />
y y<br />
/<br />
• Rectangular column: φ<br />
y<br />
= 2.10ε<br />
y<br />
/ hc<br />
• Rectangular cantilever walls: φ<br />
y<br />
= 2.00ε<br />
y<br />
/ lw<br />
• T-Section Beams: φ<br />
y<br />
= 1.70ε<br />
y<br />
/ hb<br />
Concrete Frames:<br />
Steel Frames:<br />
θ = 0. 5ε<br />
y<br />
y<br />
θ = 0. 65ε<br />
y<br />
y<br />
l<br />
h<br />
b<br />
b<br />
l<br />
h<br />
b<br />
b<br />
17
FORCE-REDUCTION FACTORS IN DIFFERENT<br />
COUNTRIES<br />
Structural Type and<br />
Material<br />
US West Coast Japan New**<br />
Zealand<br />
Europe<br />
Concrete Frame 8 1.8-3.3 9 5.85<br />
Conc. Struct. Wall 5 1.8-3.3 7.5 4.4<br />
Steel Frame 8 2.0-4.0 9 6.3<br />
Steel EBF* 8 2.0-4.0 9 6.0<br />
Masonry Walls 3.5 6 3.0<br />
Timber (struct. Wall) 2.0-4.0 6 5.0<br />
Prestressed Wall 1.5 - - -<br />
Dual Wall/Frame 8 1.8-3.3 6 5.85<br />
Bridges 3-4 3.0 6 3.5<br />
* Eccentrically Braced Frame **S P factor of 0.67 incorporated.<br />
18
FRAME DUCTILITY LIMITS<br />
NOTE: CODES LIMIT DRIFT TO 0.02-0.025<br />
Yield Drift:<br />
θ = 0. 5ε<br />
Example: l b = 6m, h b =0.6m, f y = 500MPa<br />
ε y = 500/200,000 = 0.0025;<br />
y<br />
y<br />
l<br />
h<br />
b<br />
b<br />
θ y = 0.5*0.0025*6.0/0.6 = 0.0125<br />
Thus ductility limit is 1.6 to 2.0<br />
Note: using high-strength reinforcement<br />
provides no benefit in reduced steel content!<br />
19
2. DIRECT <strong>DISPLACEMENT</strong> -<br />
<strong>BASED</strong> <strong>SEISMIC</strong> <strong>DESIGN</strong><br />
A RATIONAL <strong>SEISMIC</strong> <strong>DESIGN</strong><br />
APPROACH<br />
20
FORMULATION OF THE DIRECT<br />
<strong>DISPLACEMENT</strong>-<strong>BASED</strong> (DDBD)<br />
APPROACH<br />
DDBD is based on the observation that damage is directly<br />
related to strain (structural effects) or drift (nonstructural<br />
effects), and both can be integrated to obtain<br />
displacements. Hence damage and displacement can be<br />
directly related. The design approach ACHIEVES a<br />
specified damage limit state.<br />
It is not possible to formulate an equivalent relationship<br />
between strength (force) and damage. This is one of the<br />
major deficiencies of current force-based seismic design).<br />
The level of damage is uncertain<br />
21
ELASTIC RESPONSE OF STRUCTURES<br />
1<br />
0.5<br />
Acceleration a(T) (g)<br />
0.8<br />
0.6<br />
0.4<br />
0.2<br />
Force-based design<br />
Displacement ∆(T) (m)<br />
0.4<br />
0.3<br />
0.2<br />
0.1<br />
DDBD<br />
0<br />
0 1 2 3 4 5<br />
Period T (seconds)<br />
(a) Acceleration Spectrum for 5% damping<br />
0<br />
0 1 2 3 4 5<br />
Period T (seconds)<br />
(b Displacement Spectrum for 5% damping<br />
Elastic, Force Based: F = m.a(T).g; D = F/K<br />
Elastic, Displ. Based: F = K.D(T)<br />
22
COMPARISON OF ELASTIC FORCE AND<br />
<strong>DISPLACEMENT</strong>-<strong>BASED</strong> <strong>DESIGN</strong><br />
We require to know force (F) and displacement (∆)<br />
FORCE <strong>BASED</strong>: F =m.a (T) .g<br />
Calculate K,T,a (T) , F,∆<br />
∆= F/K<br />
(5 steps)<br />
<strong>DISPLACEMENT</strong> <strong>BASED</strong>: F = K.∆ (T)<br />
Calculate K,T,∆ (T) ,F<br />
(4 steps)<br />
23
FUNDAMENTALS OF DDBD<br />
F<br />
m e<br />
h e<br />
F u<br />
F n<br />
K e<br />
K i<br />
∆y ∆d<br />
(a) SDOF Simulation (b) Effective Stiffness K e<br />
Damping (%)<br />
0.25<br />
0.2<br />
0.15<br />
0.1<br />
0.05<br />
←<br />
Elasto-Plastic<br />
Steel Frame<br />
Concrete Frame<br />
Concrete Bridge<br />
Hybrid Prestress<br />
Displacement (m)<br />
0.5<br />
0.4<br />
0.3<br />
0.2<br />
0.1<br />
∆ d<br />
→<br />
5%<br />
10%<br />
15%<br />
20%<br />
30%<br />
0<br />
0 2 4 6<br />
Displacement Ductility<br />
↑<br />
(c) Equivalent damping vs. ductility<br />
0<br />
↓<br />
T e<br />
0 1 2 3 4 5<br />
Period (seconds)<br />
(d) Design Displacement Spectra<br />
24
Damping (%)<br />
0.25<br />
0.2<br />
0.15<br />
0.1<br />
0.05<br />
←<br />
Elasto-Plastic<br />
Steel Frame<br />
Concrete Frame<br />
Concrete Bridge<br />
Hybrid Prestress<br />
Displacement (m)<br />
0.5<br />
0.4<br />
0.3<br />
0.2<br />
0.1<br />
∆ d<br />
→<br />
5%<br />
10%<br />
15%<br />
20%<br />
30%<br />
0<br />
↑<br />
0<br />
↓<br />
T e<br />
0 2 4 6<br />
Displacement Ductility<br />
0 1 2 3 4 5<br />
Period (seconds)<br />
(c) Equivalent damping vs. ductility<br />
(d) Design Displacement Spectra<br />
Limit State Displacement; Ductility Damping<br />
Damping+Displacement T e ; K=4π 2 m e /T e<br />
2<br />
25
m e F u<br />
F F n rK i<br />
H e K i K e<br />
Limit State Displacement; Ductility Damping<br />
Damping+Displacement Te; K=4π 2 me/T e<br />
2<br />
∆ y ∆ d<br />
F u = K e ∆ d<br />
26
ELEMENTS OF DDBD: Multi-storey Building<br />
Effective Stiffness:<br />
K<br />
e<br />
=<br />
2 2<br />
4π<br />
me<br />
/ Te<br />
Base Shear Force:<br />
F<br />
=<br />
V Base<br />
= K e<br />
∆<br />
d<br />
MDOF Design Displacement:<br />
∆<br />
d<br />
=<br />
n<br />
∑<br />
i=<br />
1<br />
n<br />
( m ∆<br />
2 ) ∑( ∆ )<br />
i i<br />
/ mi<br />
i<br />
i=<br />
1<br />
Effective Mass:<br />
m<br />
n<br />
= ∑<br />
e<br />
m i<br />
i=<br />
1<br />
( ∆ )<br />
i<br />
/ ∆d<br />
Effective Height:<br />
H<br />
e<br />
=<br />
n<br />
∑<br />
i=<br />
1<br />
( m ) ∑<br />
i∆iH<br />
i<br />
/ ( mi∆i<br />
)<br />
n<br />
i=<br />
1<br />
27
3. EQUIVALENT VISCOUS DAMPING<br />
Relationships between displacement ductility and<br />
equivalent viscous damping have been determined by<br />
extensive inelastic time-history analyses, using two<br />
different approaches:<br />
• “Real” accelerograms, matching displacement of<br />
equivalent elastic system to inelastic displacement,<br />
on a record-by-record approach, then averaging the<br />
EVD over a very large number of records.<br />
• Spectrum compatible accelerograms averaging the<br />
inelastic response, and matching average equivalent<br />
elastic displacement.<br />
Results were nearly identical<br />
28
F F y<br />
βF y<br />
BASIC HYSTERESIS RULES CONSIDERED<br />
F<br />
F<br />
rk i<br />
k i k i<br />
∆<br />
∆<br />
(a) Elasto-plastic (EPP)<br />
(b) Bi-linear, r = 0.2 (BI)<br />
F<br />
k i<br />
k i µ −α<br />
∆<br />
F<br />
k i<br />
∆<br />
k i µ −α<br />
(c) Takeda “Thin” (TT) (d) Takeda “Fat” (TF)<br />
k i<br />
∆<br />
k i<br />
∆<br />
(e) Ramberg-Osgood (RO) (f) Flag Shaped (FS)<br />
29
RELATIONSHIPS FOR TANGENT-STIFFNESS<br />
DAMPING<br />
Concrete Wall Building, Bridges (TT):<br />
Concrete Frame Building (TF):<br />
Steel Frame Building (RO):<br />
Hybrid Prestressed Frame (FS,β=0.35):<br />
Friction Slider (EPP):<br />
Bilinear Isolation System (BI, r=0.2):<br />
ξ<br />
ξ<br />
ξ<br />
ξ<br />
ξ<br />
ξ<br />
eq<br />
eq<br />
eq<br />
eq<br />
eq<br />
eq<br />
⎛ µ −1⎞<br />
= 0.05 + 0.444⎜<br />
⎟<br />
⎝ µπ ⎠<br />
⎛ µ −1⎞<br />
= 0.05 + 0.565⎜<br />
⎟<br />
⎝ µπ ⎠<br />
⎛ µ −1⎞<br />
= 0.05 + 0.577⎜<br />
⎟<br />
⎝ µπ ⎠<br />
⎛ µ −1⎞<br />
= 0.05 + 0.186⎜<br />
⎟<br />
⎝ µπ ⎠<br />
⎛ µ −1⎞<br />
= 0.05 + 0.670⎜<br />
⎟<br />
⎝ µπ ⎠<br />
⎛ µ −1⎞<br />
= 0.05 + 0.519⎜<br />
⎟<br />
⎝ µπ ⎠<br />
30
4<br />
GENERAL FORM OF ELASTIC 5% <strong>DISPLACEMENT</strong><br />
SPECTRUM, FROM EC8<br />
∆ max<br />
Plateau<br />
∆ max<br />
T C Period T D T E<br />
∆ PG<br />
Displacement<br />
Corner<br />
Period<br />
Linear<br />
∆ PG<br />
T C Period T D T E<br />
31
.<strong>DESIGN</strong> <strong>DISPLACEMENT</strong> SPECTRA (1)<br />
• Can be approximately generated from design<br />
acceleration spectra (5% damping) using accelerationdisplacement<br />
relationships:<br />
∆ (T,5) = (T 2 /4π 2 ).g.a (T,5)<br />
• Values for damping other than 5% can be generated<br />
from relationships such as:<br />
∆<br />
T , ξ<br />
= ∆<br />
T ,5<br />
⋅<br />
⎛<br />
⎜<br />
⎝<br />
2<br />
7 ⎞ ⎟⎠<br />
+ ξ<br />
0.5<br />
“Normal” records, EC8 1998<br />
∆<br />
T , ξ<br />
= ∆<br />
T ,5<br />
⋅<br />
⎛<br />
⎜<br />
⎝<br />
2<br />
7 ⎞ ⎟⎠<br />
+ ξ<br />
0.25<br />
“Velocity pulse” records (Forward<br />
directionality) (tentative!)<br />
32
<strong>DESIGN</strong> <strong>DISPLACEMENT</strong> SPECTRA (4)<br />
• Based on Faccioli’s observations,the corner period T c<br />
appears to increase almost linearly with moment<br />
magnitude. For earthquakes with M W > 5.7, the<br />
following expression seems conservative:<br />
( 5.7)<br />
T 1.0<br />
+ 2.5 M −<br />
c<br />
=<br />
w<br />
seconds<br />
• Peak displacement at the corner period can be<br />
estimated from the following expression (firm ground):<br />
δ<br />
max<br />
=<br />
10<br />
( M −3.2)<br />
W<br />
r<br />
mm<br />
r = nearest<br />
distance to fault<br />
plane (km)<br />
33
Spectral Displacement (mm)<br />
2000<br />
1600<br />
1200<br />
800<br />
400<br />
0<br />
M = 7.5<br />
M = 7.0<br />
M = 6.5<br />
M = 6.0<br />
0 2 4 6 8 10<br />
Period (seconds)<br />
5% Damped Spectra Resulting from the<br />
Equations, at r = 10km<br />
34
Spectral Displacement (mm)<br />
2000<br />
1600<br />
1200<br />
800<br />
400<br />
0<br />
M = 7.5<br />
M = 7.0<br />
M = 6.5<br />
0 2 4 6 8 10<br />
Period (seconds)<br />
5% Damped spectra, Resulting from the<br />
Equations, at r = 20 km<br />
35
Spectral Displacement (mm)<br />
2000<br />
1600<br />
1200<br />
800<br />
400<br />
0<br />
M = 7.5<br />
M = 7.0<br />
M = 6.5<br />
0 2 4 6 8 10<br />
Period (seconds)<br />
5% Damped spectra Resulting from the<br />
Equations, at r = 40 km<br />
36
INFLUENCE OF DAMPING AND DUCTILITY ON<br />
SPECTRAL <strong>DISPLACEMENT</strong> RESPONSE<br />
Current EC8:<br />
1998 EC8:<br />
Newmark and Hall 1987:<br />
∆<br />
∆<br />
∆<br />
T , ξ<br />
T , ξ<br />
=<br />
∆<br />
= ∆<br />
T ,5<br />
T ,5<br />
⋅<br />
⋅<br />
⎛<br />
⎜<br />
⎝<br />
⎛<br />
⎜<br />
⎝<br />
10 ⎞ ⎟⎠<br />
5 + ξ<br />
2<br />
7 ⎞ ⎟⎠<br />
+ ξ<br />
0.5<br />
0.5<br />
( 1.31 ln )<br />
.ξ<br />
ξ<br />
= ∆T<br />
,5<br />
T ,<br />
−<br />
Independent analyses by Priestley et al, Kowalsky et al, Sullivan et<br />
al, support the 1998 EC8, not the 2003 Eqn,nor Newmark and Hall.<br />
Tentative Expression<br />
for Forward Directivity,<br />
Near field<br />
∆<br />
T , ξ<br />
= ∆<br />
T ,5<br />
⋅<br />
⎛<br />
⎜<br />
⎝<br />
2<br />
7 ⎞ ⎟⎠<br />
+ ξ<br />
0.25<br />
37
Recommended Spectral correction for Damping<br />
Relative Displacement ∆ T,ξ<br />
/∆ 4,5%<br />
1<br />
0.8<br />
0.6<br />
0.4<br />
0.2<br />
0<br />
(Eq.(2.8))<br />
ξ= 0.05<br />
ξ= 0.10<br />
ξ= 0.15<br />
ξ= 0.20<br />
ξ= 0.30<br />
Relative Displacement ∆ T,ξ<br />
/∆ 4,5%<br />
1<br />
0.8<br />
0.6<br />
0.4<br />
0.2<br />
0<br />
(Eq.(2.11))<br />
ξ= 0.05<br />
ξ= 0.10<br />
ξ= 0.15<br />
ξ= 0.20<br />
ξ= 0.30<br />
0 1 2 3 4 5<br />
Period T (seconds)<br />
(a) "Normal" Conditions<br />
0 1 2 3 4 5<br />
Period T (seconds)<br />
(b) Velocity Pulse Conditions<br />
K e =4π 2 m e /T e<br />
2<br />
; V base =K e ∆ d<br />
38
SCOPE OF RESEARCH AND BOOK<br />
The research study (and the text book) considered<br />
the following structural systems:<br />
• Frames (concrete, steel, infilled, braced, precast)<br />
• Structural walls (cantilever and coupled)<br />
• Dual Wall/Frame structures<br />
• Timber structures<br />
• Unreinforced masonry buildings<br />
• Structures with Seismic Isolation and added<br />
damping<br />
• Bridges<br />
• Marginal wharves<br />
39
CHAPTER 4<br />
ANALYSIS TOOLS FOR DIRECT<br />
<strong>DISPLACEMENT</strong>-<strong>BASED</strong> <strong>DESIGN</strong><br />
Deals with a number of particularly relevant issues:<br />
• Moment-curvature analysis (Cumbia on CD)<br />
• Equilibrium considerations<br />
• Section stiffness<br />
• Shear strength<br />
• Capacity design analyses<br />
• Inelastic time-history analyses (Ruaumoko, SeismoStruct<br />
on CD)<br />
• Pushover analyses (Ruaumoko, SeismoStruct)<br />
40
CHAPTER 5<br />
FRAME BUILDINGS<br />
Considers issues specially relevant to design of frames:<br />
• design displacement profiles<br />
• one way/two way frames<br />
• irregular frames<br />
• elastic response<br />
• combination with gravity-load effects (consider<br />
separately!<br />
• capacity design for columns, and beams<br />
• hybrid precast frames<br />
41
CHAPTER 6<br />
STRUCTURAL WALL BUILDINGS<br />
Issues specially relevant to wall buildings considered:<br />
• Yield displacement and elastically responding walls<br />
• Torsional response<br />
• Capacity design effects<br />
• Foundation rotational stiffness<br />
• Coupled wall design (based on equilibrium, not elastic<br />
stiffness)<br />
42
CHAPTER 7<br />
DUAL WALL/FRAME BUILDINGS<br />
(a) Plan View<br />
(b) Long Direction Model<br />
Issues: How to distribute lateral<br />
force between walls and frames<br />
(a designer’s choice –not based<br />
on elastic stiffness)<br />
How to distribute shear up the<br />
frame (also a designer’s choice)<br />
Analysis for design requires no<br />
information about relative<br />
stiffnesses, which are, in fact<br />
irrelevant.<br />
(c) Short Direction Model<br />
43
CHAPTER 8<br />
MASONRY BUILDINGS<br />
This chapter essentially deals with unreinforced, or very<br />
lightly reinforced buildings, such as are used extensively in<br />
Europe and Central and South America. Displacementbased<br />
design is a much more rational way of designing such<br />
structures than current force-based approaches. Coupling<br />
between walls by floor slabs and spandrels is rationally<br />
considered with an innovative design approach<br />
44
Chapter 9: DUCTILE TIMBER STRUCTURES<br />
F<br />
Joint<br />
Framing<br />
Shear<br />
Panel<br />
End View<br />
(a) Ductile Moment-Resisting Frame (b) Timber Shear Panel Bracing<br />
Ductile<br />
connectors<br />
Post-tensioning<br />
P<br />
P<br />
(c) Post-tensioned Timber Frame<br />
45
CHAPTER 10<br />
BRIDGES<br />
Consideration of aspects specially applicable to bridges:<br />
• Longitudinal/transverse design<br />
• Elastically responding bridges<br />
• Influence of bearings and foundation flexibility<br />
• P-∆ Effects<br />
• Different foundation conditions<br />
• Capacity design (Effective modal superposition)<br />
46
Isolator<br />
Isolated rigid<br />
structure<br />
Braced frame<br />
with added<br />
damping<br />
Isolated bridge<br />
Partially isolated bridge<br />
Foundation<br />
sliding on gravel<br />
layer<br />
Pier<br />
Gravel<br />
layer Soil<br />
Concrete<br />
Chapter 11<br />
ISOLATION<br />
Deck<br />
Rocking bridge bent<br />
47
CHAPTER 12<br />
WHARVES AND PIERS<br />
Design is dominated by soil/structure interaction effects<br />
Displacement-based design, to specified limit-strains in<br />
piles (two-level design)<br />
Torsional response is critical<br />
This chapter is the basis of the POLA seismic design code<br />
48
INELASTIC FORCE-<strong>DISPLACEMENT</strong> RESPONSE<br />
FROM PUSHOVER ANALYSIS<br />
Wharf Deck<br />
F E D C B A<br />
T F T E T D T C T B T A<br />
F L<br />
L Cl<br />
Ground<br />
L sp<br />
IG F<br />
IG E<br />
IG D<br />
IG C<br />
IG B<br />
IG A<br />
Piles<br />
Inelastic pile<br />
members<br />
Inelastic Soil<br />
Springs<br />
x F<br />
x E<br />
x D<br />
x C<br />
x B<br />
x A<br />
49
CHAPTER 13<br />
<strong>DISPLACEMENT</strong>-<strong>BASED</strong> <strong>SEISMIC</strong> ASSESSMENT<br />
The principles of displacement-based design are adapted to<br />
assessment of existing structures. Both buildings and<br />
bridges are considered in developing the topic, and in the<br />
design examples<br />
50
MDOF PLASTIC MECHANISMS<br />
5<br />
4<br />
3<br />
2<br />
1<br />
Height<br />
Limit state<br />
∆ P,c<br />
Yield<br />
Plastic mechanism<br />
Displacement<br />
(a) Beam Sway, S i < 0.85, all levels (b) Beam Sway Displacement Profiles<br />
5<br />
4<br />
3<br />
2<br />
Height<br />
Yield<br />
Column sway<br />
at Level 1<br />
Column sway<br />
at Level 2<br />
1<br />
∆ P<br />
Plastic mechanism<br />
Displacement<br />
(c) Column Sway, S i > 1, Levels 1 or 2 (d) Column Sway Displacement<br />
51
CHAPTER 14<br />
DRAFT <strong>DISPLACEMENT</strong>-<strong>BASED</strong> CODE FOR<br />
<strong>SEISMIC</strong> <strong>DESIGN</strong> OF BUILDINGS<br />
Intended as a starting point for development of design<br />
codes.<br />
52
DIRECT DISPLACEMEMENT-<strong>BASED</strong> <strong>DESIGN</strong><br />
<strong>DESIGN</strong> <strong>DISPLACEMENT</strong><br />
Damage is strain dependent. (e.g. onset of concrete<br />
crushing: strain = 0.004, residual crack widths require<br />
grouting if peak reinforcement strain exceeds 0.015).<br />
From strains we can calculate curvature. We can<br />
integrate curvature to find displacement.<br />
Thus we can directly relate structural damage to<br />
displacement<br />
Non-structural damage can generally be related to<br />
drift (Drift = interstorey displacement divided by<br />
interstorey height). Drift can be integrated to find<br />
displacement.<br />
Thus we can relate non-structural damage to<br />
displacement<br />
53
EXAMPLE OF STRAIN LIMIT STATES<br />
Curvature from concrete<br />
compression:<br />
φ mc = ε cm /c<br />
Curvature from reinforcement<br />
tension:<br />
φ ms = ε sm /(d-c)<br />
Chose lesser of φ mc and φ ms ,<br />
Design Displacement is:<br />
∆ ds = ∆ y + ∆ p<br />
= φ y H 2 /3 + (φ m -φ y )L p H<br />
L p = plastic hinge length.<br />
54
CRITICAL <strong>DISPLACEMENT</strong>S<br />
•Frames: normally governed by structural or nonstructural<br />
drift in beams of lowest storey<br />
• Cantilever Wall buildings: normally governed by<br />
plastic rotation at the wall base (for longest wall),<br />
or drift in top storey<br />
• Bridges: normally governed by plastic rotation,<br />
or drift limit, of the shortest column<br />
55
FRAMES<br />
1.0<br />
n=4:<br />
δ<br />
i<br />
=<br />
H /<br />
i<br />
H<br />
n<br />
H/H n<br />
n>4:<br />
δ =<br />
i<br />
4<br />
3<br />
⎛<br />
⋅<br />
⎜<br />
⎝<br />
H<br />
H<br />
i<br />
n<br />
⎞ ⎛ ⎟ ⋅ ⎜1<br />
−<br />
⎠ ⎝<br />
Hi<br />
4H<br />
n<br />
⎞<br />
⎟<br />
⎠<br />
Mode displ. 1.0<br />
(Based on results of inelastic timehistory<br />
analysis. Note, in some cases<br />
it may be necessary to review the<br />
displacement profile after initial<br />
analysis)<br />
56
CANTILEVER WALL <strong>DESIGN</strong> PROFILES:<br />
If roof drift is less than the code drift limit θ c , the<br />
design displacement profile is:<br />
∆<br />
i<br />
= ∆<br />
yi<br />
+ ∆<br />
pi<br />
=<br />
ε y ⎛ H ⎞ ⎛<br />
i<br />
y<br />
Hi<br />
m<br />
lw<br />
H<br />
+ ε<br />
⎜ − ⎟<br />
⎜φ<br />
−<br />
2<br />
2<br />
1<br />
⎝ 3<br />
n ⎠ ⎝ lw<br />
⎟ ⎞<br />
L<br />
⎠<br />
p<br />
H<br />
i<br />
If the code drift limit governs the roof drift, the design<br />
displacement profile is:<br />
∆<br />
i<br />
= ∆<br />
yi<br />
+<br />
( − )<br />
y<br />
i<br />
y n<br />
H =<br />
2<br />
θ θ H ⎜1<br />
⎟ ⎜θc<br />
− Hi<br />
c<br />
yn<br />
i<br />
ε<br />
l<br />
w<br />
i<br />
⎛<br />
⎜ −<br />
⎝<br />
H<br />
3H<br />
n<br />
⎞ ⎛<br />
⎟ + ⎜<br />
⎠ ⎝<br />
ε H<br />
l<br />
w<br />
⎟ ⎞<br />
⎠<br />
57
BRIDGE CHARACTERISTIC MODE SHAPES<br />
∆<br />
∆ 1<br />
∆<br />
∆ 2<br />
∆ 3<br />
∆ 4<br />
∆ 5<br />
∆ 1<br />
∆ 2<br />
∆<br />
∆ 3<br />
∆<br />
∆<br />
(a) Symm., Free abuts. (b) Asymm., Free abuts. (c) Symm., free abuts.<br />
Rigid SS translation Rigid SS translation+rotation Flexible SS<br />
∆ 1 ∆ 1 ∆ 1<br />
∆ 2 ∆ 2 ∆ 2<br />
∆ 3 ∆ 3 ∆ 3<br />
∆ 4<br />
∆ 4 ∆ 4 ∆ 4<br />
∆ 5<br />
∆ 5<br />
∆ 5<br />
∆ 5<br />
(d) Symm,. Restrained abuts. (e) Internal movement joint (f) Free abuts., M.joint<br />
Flexible SS Rigid SS, Restrained abuts. Flexible SS<br />
58
ELASTIC RESPONSE OF FRAMES<br />
The shape of the displacement spectrum, with a peak displacement<br />
plateau, implies that in regions of moderate seismicity, tall frames<br />
will respond elastically<br />
Assuming start of the constant velocity slope of acceleration<br />
spectrum at T = 0.5 sec, and peak spectral acceleration = 2.5<br />
times PGA, then the plateau displacement can be written as:<br />
∆<br />
TC<br />
=<br />
0.031×<br />
PGA(1<br />
+ 2.5( M −1))<br />
W<br />
Taking a typical frame of n storeys with beam length/depth =10,<br />
f ye = 400MPa the equivalent yield displacement can be approximated<br />
as<br />
∆<br />
y<br />
= θ<br />
y.( 0.7×<br />
3.5n)<br />
= 0.01×<br />
0.7×<br />
3.5n<br />
= 0. 0245n<br />
59
1.6<br />
Displacement (m)<br />
1.2<br />
0.8<br />
0.4<br />
0<br />
Yield<br />
displacement<br />
Peak elastic spectral<br />
Displacement<br />
0.7g<br />
0.6g<br />
0.5g<br />
0.4g<br />
0.3g<br />
0.2g<br />
0.1g<br />
24 storeys<br />
20 storeys<br />
16 stories<br />
12 storeys<br />
8 storeys<br />
4 storeys<br />
6 6.4 6.8 7.2 7.6 8<br />
Moment Magnitude, M W<br />
60
DRIFT-LIMITED DUCTILITY FOR WALLS<br />
Maximum Design Ductility (µ)<br />
10<br />
8<br />
6<br />
4<br />
2<br />
0<br />
θ c =0.02<br />
Elastic<br />
θ c =0.025<br />
2 4 6 8 10<br />
Wall Aspect Ratio (A r =H n /l w )<br />
Maximum Design Ductility (µ)<br />
10<br />
8<br />
6<br />
4<br />
2<br />
0<br />
θ c =0.02<br />
Elastic<br />
θ c =0.02<br />
2 4<br />
Wall Aspec<br />
(a) Yield Drift = ε y A r (b) Yield Drift =<br />
61
ANALYSIS OF FRAMES UNDER LATERAL FORCES<br />
F 4 V B4 V B4<br />
Level 4<br />
Base Overturning Moment<br />
F 2<br />
F 3 V B3 V B3<br />
V B2 V B2<br />
Level 3<br />
Level 2<br />
OTM<br />
OTM<br />
OTM<br />
∑<br />
= Fi<br />
⋅ H<br />
i<br />
= T ⋅ Lb<br />
+<br />
= V ⋅ L<br />
∑<br />
Bi<br />
∑<br />
base<br />
M<br />
+<br />
Cj<br />
∑<br />
M<br />
Cj<br />
V B1 V B1<br />
F 1 Level 1<br />
V C1 V C2 V C3<br />
0.6H 1<br />
M C1 M C2 M C3<br />
T C<br />
L base<br />
Level 0<br />
H 3<br />
Lateral force distribution<br />
F<br />
i<br />
=<br />
V<br />
B<br />
( m ∆ ) ∑( ∆ )<br />
i i<br />
/ mi<br />
i<br />
n<br />
i=<br />
1<br />
62
PLASTIC <strong>DISPLACEMENT</strong> OF CANTILEVER WALLS<br />
l W<br />
( )<br />
Plastic<br />
Hinge<br />
H e<br />
∆ p<br />
L P<br />
L SP<br />
θ p<br />
0.5L P -L SP<br />
P<br />
φ p φ y<br />
(a) Wall (b) Curvature (c) Plastic Displacement<br />
P<br />
P<br />
( H − 0.5L<br />
− L ) = θ ( H − ( 0. L − L ))<br />
∆ = φ L<br />
5<br />
∆<br />
P<br />
P<br />
P<br />
e<br />
= φ L H = θ H<br />
P<br />
e<br />
P<br />
P<br />
e<br />
e<br />
SP<br />
63<br />
plastic hinge length: L = k ⋅ H + 0. 1l<br />
+ L k = 0.2(fu/fy – 1) =0.08<br />
W<br />
P<br />
SP<br />
e<br />
P<br />
SP<br />
(acceptable approximation)
LIMIT STATE CURVATURES FOR WALLS:<br />
From analyses:<br />
• Serviceability curvature:<br />
• Damage Control curvature:<br />
φ s<br />
⋅l<br />
w<br />
= 0.0175<br />
φ dc<br />
⋅l<br />
w<br />
= 0.072<br />
In both cases steel strain limit dominates. A general equation can be<br />
written:<br />
• General limit curvature:<br />
φ ⋅ =1.2ε<br />
ls<br />
l<br />
w s,<br />
ls<br />
Design Displacement<br />
profile is thus:<br />
ε H<br />
2<br />
y i ⎛ ∆<br />
i = ∆<br />
yi + ∆<br />
pi =<br />
l<br />
⎜1<br />
−<br />
w<br />
3<br />
⎝<br />
H<br />
i<br />
H<br />
n<br />
⎞<br />
⎟ + θ<br />
pH<br />
⎠<br />
i<br />
64
TORSIONAL RESPONSE OF WALL BUILDINGS WITH<br />
STRENGTH AND STIFFNESS ECCENTRICITY<br />
Z<br />
Wall 4<br />
k trans<br />
L Z =15m<br />
k Z1,<br />
C R<br />
C V<br />
Wall C M<br />
Wall 2<br />
V 1<br />
e VX Strength V2<br />
e RX<br />
V<br />
eccentricity<br />
Stiffness<br />
B<br />
k<br />
eccentricity<br />
trans<br />
Wall 3<br />
L X = 25 m<br />
k Z2<br />
X<br />
Both strength and stiffness eccentricity affect torsional response.<br />
In DDBD the design displacement at centre of mass is reduced to<br />
account for torsional response<br />
65
COUPLED WALLS -TYPICAL ELEVATION<br />
F i<br />
H i<br />
Gravity<br />
Frame<br />
1 2<br />
Coupled<br />
Walls<br />
(a) Structure and Lateral Forces<br />
66
COUPLING BEAM DRIFTS<br />
reinforcement<br />
Conventional<br />
θ W<br />
θ CB<br />
0.5l W L CB 0.5l W<br />
Diagonal<br />
reinforcement<br />
α<br />
α<br />
(a) Drift Geometry (b) Coupling Beam<br />
θ<br />
CB<br />
= θ<br />
W<br />
( 1+ l / L )<br />
W<br />
CB<br />
67
CAPACITY <strong>DESIGN</strong><br />
• Overstrength: Material strengths will generally<br />
exceed dependable strengths used for design;<br />
confinement and strain-hardening further<br />
increase flexural strength above design strength<br />
• Higher mode effects: Either not considered<br />
(equivalent lateral force approach), or incorrectly<br />
considered (elastic modal superposition) in current<br />
design.<br />
68
STRUCTURAL WALL<br />
FAILURE<br />
Inadequate transverse<br />
reinforcement in plastic<br />
hinge region<br />
69<br />
KOBE, 1995
INADEQUATE CONSIDER-<br />
ATION OF HIGHER MODE<br />
EFFECTS<br />
Hinge forms above base<br />
70<br />
VALPARAISO, 1985
HIGHER MODE EFFECTS<br />
Two effects in DDBD<br />
1. Drift amplification – A reduction to the design drift<br />
is applied to frames higher than about 10 storeys<br />
2. Moment and Shear amplification for capacityprotected<br />
actions and members. These have been<br />
extensively researched by inelastic time-history<br />
analysis. Results are found to depend on the effective<br />
structural displacement ductility demand. New design<br />
equations and simplified design approaches have been<br />
developed for different structural systems.<br />
71
EFFECTIVE MODAL SUPERPOSITION FOR<br />
HIGHER MODE EFFECTS<br />
A modal analysis procedure combining the inelastic<br />
first mode and ELASTIC higher modes by a SRSS<br />
approach provides good simulation of higher mode<br />
effects. The agreement is improved if the stiffness<br />
of plastic hinges is reduced to reflect the design<br />
ductility<br />
i.e. use EI/µ for members with plastic hinges.<br />
72
60<br />
30<br />
40<br />
MMS THA MMS THA MMS THA<br />
Height (m)<br />
20<br />
10<br />
Height (m)<br />
30<br />
20<br />
10<br />
Height (m)<br />
40<br />
20<br />
0<br />
0 500 1000 1500 2000 2500 3000<br />
0<br />
0<br />
0 1000 2000 3000 4000<br />
0 1000 2000 3000 4000<br />
Shear Force (kN)<br />
Shear Force (kN)<br />
Shear Force (kN)<br />
(m) Twelve-Storey Wall, IR=0.5 (q) Sixteen-Storey Wall, IR=0.5 (u) Twenty-Storey Wall, IR=0.5<br />
60<br />
30<br />
40<br />
Height (m)<br />
20<br />
10<br />
MMS THA<br />
Height (m)<br />
30<br />
20<br />
10<br />
THA MMS<br />
Height (m)<br />
40<br />
20<br />
THA MMS<br />
0<br />
0 500 1000 1500 2000 2500 3000<br />
0<br />
0<br />
0 1000 2000 3000 4000<br />
0 1000 2000 3000 4000<br />
Shear Force (kN)<br />
Shear Force (kN)<br />
Shear Force (kN)<br />
(n) Twelve-Storey Wall, IR=1.0 (r) Sixteen-Storey Wall, IR=1.0 (v) Twenty-Storey Wall, IR=1.0<br />
60<br />
MMS Shear Envelopes Compared with Time History Results<br />
30<br />
40<br />
for Different Seismic Intensity Ratios (IR=1= Design)<br />
ht (m)<br />
20<br />
ht (m)<br />
30<br />
ht (m)<br />
40<br />
83 73
DOES DDBD MAKE A DIFFERENCE<br />
• Determining moment demand by elastic modal<br />
analysis is inappropriate, resulting in poor<br />
distributions of lateral strength<br />
• Force-based design uses elastic stiffness which is<br />
NOT KNOWN at the start of the design. DDBD uses<br />
yield displacement or drift which IS known at the<br />
start of the design.<br />
• DDBD achieves a specified limit state at the design<br />
intensity; force-based design, at best, is bounded by<br />
the limit state, and vulnerability to damage is<br />
variable.<br />
• The design effort with DDBD is less than with<br />
force-based design.<br />
74
INFLUENCE OF <strong>SEISMIC</strong> INTENSITY ON <strong>DESIGN</strong><br />
FORCES<br />
Force-Based Design Displacement-Based Design<br />
V<br />
Z<br />
e 2<br />
=<br />
e1<br />
, but<br />
2<br />
b 2<br />
= V<br />
Z2<br />
b1<br />
Z<br />
Hence: K<br />
1<br />
e<br />
If Z 2<br />
= 0.5Z 1<br />
, V b2<br />
= 0.5V b1<br />
Hence:<br />
T<br />
T<br />
Z<br />
1<br />
V<br />
=<br />
K<br />
K<br />
e<br />
⎛ Z<br />
⎜<br />
=<br />
⎞<br />
2<br />
2 1 ⎟ e ⎜<br />
⎝ Z1<br />
⎠<br />
2<br />
= V<br />
⎛ Z<br />
⎜<br />
⎝<br />
⎞<br />
2<br />
2 1 ⎟ B B ⎜ Z1<br />
⎠<br />
2 2<br />
4π<br />
me<br />
/ Te<br />
2<br />
: V 75 b2<br />
= 0.25V b1
BRIDGE COLUMNS OF UNEQUAL HEIGHT<br />
`<br />
F H c<br />
H A H B H C<br />
H A<br />
C<br />
H B<br />
A<br />
B<br />
Force-Based Design Displacement-Based Design<br />
∆<br />
Stiffness: prop. to 1/H 3 prop. to 1/H<br />
Shear Force: prop. to 1/H 3 prop. to 1/H<br />
Moments: prop. to 1/H 2<br />
Rebar: prop. to 1/H 2<br />
equal<br />
equal<br />
Ductility: equal (!) prop. to 1/H 2<br />
76
CONCLUSIONS<br />
DOES DDBD MAKE A DIFFERENCE<br />
YES!<br />
Thank you<br />
77