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Tools for Performance and/or
Objective Based Structural
Fire Design
ACI Convention
Kansas City, MO April 2015
Maged A. Youssef, P.Eng.Associate Professor
Associate Chair for Undergraduate Affairs
E-mail: [email protected]
2
Design Codes and Structural Fire Engineering
• Architect and Structural Engineer
• EuroCode 2:
– estimate the fire resistance of structural elements.
– basis for advanced models at the structure level.
• 2005 NBCC:
– Objective-Based Design.
• US:
– ASCE 7 / Performance-Based Design.
3
RESEARCH OBJECTIVES
• Provide engineers with the ability to analyze structures exposed to fire
– Simple Methods (develop engineering sense).
• Develop design tools for different RC elements.
This presentation will cover the major challenges and the overall vision
4
(1) Thermal Strains
• Non-uniform distribution.
• Will the concrete section allow these strains to develop?
(Plane section!)
-600
-400
-200
0
200
400
600
800
1000
Tem
pe
ratu
re (
oC
)
305
mm
305 mmsteel bars
Fire (Bottom)
Fire (Upper)
Fire
(R
ight
)
Fire
(Lef
t)
5
(2) Temperature Distribution
Temperature o
C
200 400 600 800
He
igh
t (m
m)
-150
-75
0
75
150
T1
f ’cT1
T2
f ’cT2
T3
f ’cT3
Tav
f ’cTavT av
( t = 1 hr)
avg. Temp.
(temperature)
avg. Temp.
(strength)
Z
X
6
h
b
𝜓𝑐𝑇
-
+
z
equivalent
linear strain
nonlinear
thermal strain
thermalstrain in
top bars
thermalstrain in
bottom bars
𝜀𝑖
𝜓𝑖
- 𝜓
-
+
Fire Fire
Fire
x
y
b
h( Left ) ( Right )
( Bottom )
𝜀𝑖
𝜓𝑖
𝑀𝑎𝑝𝑝
𝜓𝑐𝑇
-
+
z
equivalent
linear strain
nonlinear
thermal strain
thermalstrain in
top bars
thermalstrain in
bottom bars
𝜀𝑖
𝜓𝑖
- 𝜓
-
+
Fire Fire
Fire
x
y
b
h( Left ) ( Right )
( Bottom )
𝜀𝑖
𝜓𝑖
𝑀𝑎𝑝𝑝
𝜀 = 𝜀𝑡ℎ + 𝜀𝑠𝑡 + 𝜀𝑐 + 𝜀𝑡𝑟 = 𝜀𝑡ℎ + 𝜀𝑐𝑇
𝜓𝑐𝑇
-
+
z
equivalent
linear strain
nonlinear
thermal strain
thermalstrain in
top bars
thermalstrain in
bottom bars
𝜀𝑖
𝜓𝑖
- 𝜓
- +
Fire Fire
Fire
x
y
b
h( Left ) ( Right )
( Bottom )
𝜀𝑖
𝜓𝑖
𝑀𝑎𝑝𝑝
𝜀𝑡ℎ
_
Thermal
Strain
Equivalent Thermal
Strain
Self-induced
Strain
𝜀 = 𝜀𝑡ℎ + 𝜀𝑠𝑡 + 𝜀𝑐 + 𝜀𝑡𝑟 = 𝜀𝑡ℎ + 𝜀𝑐𝑇
7
= f (ASTM-E119 Time, Width, Area of
Steel Bars in Tension and
Compression, Number of Layers of
Tension Steel Bars , Aggregate Size)
Fire duration (hr)
0.0 0.5 1.0 1.5 2.0 2.5
i x
10
-3 (
M+
ve)
0
2
4
6
8
i x
10
-3 (
M-v
e)
0
4
8
12
16
B7
I7
Eq. 5
Eq. 7
siliceous
(M+ve)
(M-ve)carbonate
carbonate
siliceous
Fire duration (hr)
0.0 0.5 1.0 1.5 2.0 2.5
i x 1
0-6
0
2
4
6
8
10
B7
I7
Eq. 6
Eq. 8siliceous
carbonate
siliceous
(M+ve)
(M-ve)
𝜀𝑖
(3) Unrestrained Thermal Strains= f (ASTM-E119 Time, Width, Height, Area
of Steel Bars in Tension and Compression,
Number of Layers of Tension Steel Bars ,
Aggregate Size)
M+ve: Lower tension steel properties,
need higher steel strain or lower curvature.
M-ve: Tension steel unaffected and
concrete in compression
h
b
equivalent
linear strain
nonlinear
thermal strain
thermal
strain in
top bars
thermal
strain in
bottom bars
+
+
_
𝜓 + =
_ =
𝜓𝑐𝑇
+
_
+ 𝜀𝑖
+ 𝜀𝑖
+
𝜓 𝑖
𝜓 𝑖
Fire Fire
Fire
mesh for
heat transfer
concrete and
steel layers for
x
y
b
h( Left ) ( Right )
( Bottom )
sectional analysisFire
( Top )
c) equivalent linear
thermal strain (𝜀𝑡ℎ )
b) total strain (𝜀) d) equivalent
mechanical strain (𝜀𝑐𝑇 )
f) nonlinear thermal
strain (𝜀𝑡ℎ )
a) fiber model
c) equivalent linear
thermal strain (𝜀𝑡ℎ )
e) self-induced
thermal strain (𝜀𝑠𝑡 )
𝜀 = 𝜀𝑡ℎ + 𝜀𝑠𝑡 + 𝜀𝑐 + 𝜀𝑡𝑟 = 𝜀𝑡ℎ + 𝜀𝑐𝑇
+
𝜓𝑐𝑇
- +
z
equivalent
linear strain
nonlinear
thermal strain
thermalstrain in
top bars
thermalstrain in
bottom bars
𝜀𝑖
𝜓𝑖
- 𝜓
-
+
Fire Fire
Fire
x
y
b
h( Left ) ( Right )
( Bottom )
𝜀𝑖
𝜓𝑖
𝑀𝑎𝑝𝑝
𝜓𝑐𝑇
-
+
z
equivalent
linear strain
nonlinear
thermal strain
thermalstrain in
top bars
thermalstrain in
bottom bars
𝜀𝑖
𝜓𝑖
- 𝜓
-
+
Fire Fire
Fire
x
y
b
h( Left ) ( Right )
( Bottom )
𝜀𝑖
𝜓𝑖
𝑀𝑎𝑝𝑝
Self-induced
StrainMech.
Strain
𝜀 = 𝜀𝑡ℎ + 𝜀𝑠𝑡 + 𝜀𝑐 + 𝜀𝑡𝑟 = 𝜀𝑡ℎ + 𝜀𝑐𝑇
(4) Sectional Analysis at Elevated Temperatures
Thermal Strains.
Transient Strains.
Temperature Distribution.
Temperature-dependent material properties.
9
(5)EA and EI for Fire-Exposed Elements
M nM
Fire
M+ve
M+ve
M+veP
appP nP
PP
Fire
𝜀𝑖 𝜀𝑐𝑇
𝐸𝐴𝑒𝑓𝑓
1
𝜀
𝜀𝑖 𝜀𝑐𝑇
𝐸𝐴𝑒𝑓𝑓
1
𝜀
Simplified Approach to Calculate EAeff and EIeff
10
(6) Solution Procedure for a Structure
1) Calculate primary moments & axial forces in different members.
2) Identify elements exposed to fire and use their section properties
and fire duration to evaluate , , EAeff and EIeff.
3) Convert and to elongations and rotations
4) Apply the elongations and rotations for fire-exposed elements and
calculate the secondary moments and associated axial forces.
5) Recalculate EAeff, Eieff, and the primary moments.
6) Repeat steps 4 and 5 until convergence is achieved.
𝜀𝑖
𝜀𝑖
11
The beam is divided
into segments
Eieff is calculated based
on the primary BMD
Thermal curvatures are
simulated by concentrated
rotations
Secondary moments are
generated
M1
M
S3S2S1 S1S2
S1 S2 S3
M2
M3
M1M
2
M1 M
2
M3
Fire Fire
+veM
+veM
-ve
S3S2S1 S1S2
a) beam loading and reinforcement configuration
b) primary BMD
(𝑡 = 0.0 ℎ𝑟)
c) 𝑀 − 𝜓 diagrams at fire duration ( 𝑡 )
d) 𝐸𝐼𝑒𝑓𝑓 and 𝜓𝑖
distributions at fire duration ( 𝑡 )
e) equivalent thermal moments 𝑀𝑡ℎ at 𝑡
f) secondary moments due to
thermal effect 𝑀𝑡ℎ at 𝑡
𝐸𝐼𝑒𝑓𝑓 3 𝜓𝑖 3 ×
𝑀𝑡ℎ 1 = 𝑀𝑡ℎ 3 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝑀𝑡ℎ 1 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 = 𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 =
𝜓𝑖 2
𝜓𝑖 3
𝐸𝐼𝑒𝑓𝑓 2
1
𝐸𝐼𝑒𝑓𝑓 3
1
𝜓𝑖 1
𝐸𝐼𝑒𝑓𝑓 1
1
𝜓𝑖 1
𝜓𝑖 3
𝜓𝑖 1
𝜓𝑖 2
𝜓𝑖 2
𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 3 𝐸𝐼𝑒𝑓𝑓 2 𝐸𝐼𝑒𝑓𝑓 2
M1
M
S3S2S1 S1S2
S1 S2 S3
M2
M3
M1M
2
M1 M
2
M3
Fire Fire
+veM
+veM
-ve
S3S2S1 S1S2
a) beam loading and reinforcement configuration
b) primary BMD
(𝑡 = 0.0 ℎ𝑟)
c) 𝑀 − 𝜓 diagrams at fire duration ( 𝑡 )
d) 𝐸𝐼𝑒𝑓𝑓 and 𝜓𝑖
distributions at fire duration ( 𝑡 )
e) equivalent thermal moments 𝑀𝑡ℎ at 𝑡
f) secondary moments due to
thermal effect 𝑀𝑡ℎ at 𝑡
𝐸𝐼𝑒𝑓𝑓 3 𝜓𝑖 3 ×
𝑀𝑡ℎ 1 = 𝑀𝑡ℎ 3 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝑀𝑡ℎ 1 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 = 𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 =
𝜓𝑖 2
𝜓𝑖 3
𝐸𝐼𝑒𝑓𝑓 2
1
𝐸𝐼𝑒𝑓𝑓 3
1
𝜓𝑖 1
𝐸𝐼𝑒𝑓𝑓 1
1
𝜓𝑖 1
𝜓𝑖 3
𝜓𝑖 1
𝜓𝑖 2
𝜓𝑖 2
𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 3 𝐸𝐼𝑒𝑓𝑓 2 𝐸𝐼𝑒𝑓𝑓 2
M1
M
S3S2S1 S1S2
S1 S2 S3
M2
M3
M1M
2
M1 M
2
M3
Fire Fire
+veM
+veM
-ve
S3S2S1 S1S2
a) beam loading and reinforcement configuration
b) primary BMD
(𝑡 = 0.0 ℎ𝑟)
c) 𝑀 − 𝜓 diagrams at fire duration ( 𝑡 )
d) 𝐸𝐼𝑒𝑓𝑓 and 𝜓𝑖
distributions at fire duration ( 𝑡 )
e) equivalent thermal moments 𝑀𝑡ℎ at 𝑡
f) secondary moments due to
thermal effect 𝑀𝑡ℎ at 𝑡
𝐸𝐼𝑒𝑓𝑓 3 𝜓𝑖 3 ×
𝑀𝑡ℎ 1 = 𝑀𝑡ℎ 3 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝑀𝑡ℎ 1 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 = 𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 =
𝜓𝑖 2
𝜓𝑖 3
𝐸𝐼𝑒𝑓𝑓 2
1
𝐸𝐼𝑒𝑓𝑓 3
1
𝜓𝑖 1
𝐸𝐼𝑒𝑓𝑓 1
1
𝜓𝑖 1
𝜓𝑖 3
𝜓𝑖 1
𝜓𝑖 2
𝜓𝑖 2
𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 3 𝐸𝐼𝑒𝑓𝑓 2 𝐸𝐼𝑒𝑓𝑓 2
M1
M
S3S2S1 S1S2
S1 S2 S3
M2
M3
M1M
2
M1 M
2
M3
Fire Fire
+veM
+veM
-ve
S3S2S1 S1S2
a) beam loading and reinforcement configuration
b) primary BMD
(𝑡 = 0.0 ℎ𝑟)
c) 𝑀 − 𝜓 diagrams at fire duration ( 𝑡 )
d) 𝐸𝐼𝑒𝑓𝑓 and 𝜓𝑖
distributions at fire duration ( 𝑡 )
e) equivalent thermal moments 𝑀𝑡ℎ at 𝑡
f) secondary moments due to
thermal effect 𝑀𝑡ℎ at 𝑡
𝐸𝐼𝑒𝑓𝑓 3 𝜓𝑖 3 ×
𝑀𝑡ℎ 1 = 𝑀𝑡ℎ 3 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝑀𝑡ℎ 1 =
𝜓𝑖 1 × 𝐸𝐼𝑒𝑓𝑓 1
𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 = 𝐸𝐼𝑒𝑓𝑓 2 𝜓𝑖 2 × 𝑀𝑡ℎ 2 =
𝜓𝑖 2
𝜓𝑖 3
𝐸𝐼𝑒𝑓𝑓 2
1
𝐸𝐼𝑒𝑓𝑓 3
1
𝜓𝑖 1
𝐸𝐼𝑒𝑓𝑓 1
1
𝜓𝑖 1
𝜓𝑖 3
𝜓𝑖 1
𝜓𝑖 2
𝜓𝑖 2
𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 1 𝐸𝐼𝑒𝑓𝑓 3 𝐸𝐼𝑒𝑓𝑓 2 𝐸𝐼𝑒𝑓𝑓 2
Application for a Continuous Beam
(7) Simplified Tools
• Stress-Block Parameters of RC Beams Exposed to Fire.
• Interaction Diagrams of RC Columns Exposed to Fire.
• Shear Capacity of RC Beams Exposed to Fire.
13
(8) Strain Defining Section Capacity
εc max : concrete
strain corresponds
to Moment of
Resistance Mr
A parametric study
is conducted to
evaluate εc max at
elevated temperatures
Reasonable
predictions are
obtained at r = 0.25
cT x 10-3
0 10 20 30 40
f cT
/ f
' c
0.00
0.25
0.50
0.75
1.00Tavg = 200
oC
400 oC
600 oC
= 0.02
r.
cT
ma
x
Mo
me
nt
(M)
= 0.3
Curvature ( )
= 0.0
= 0.9
= 0.6
concrete crushing
flexural capacity
i
M x 102 (kN.m)
0.0 0.5 1.0 1.5 2.0 2.5
P x 103 (kN)
0
1
2
3
4r = 1.0(peak points)
r = 0.0
r = 0.25
r = 0.50
r = 0.75
r = 1.0
Flexural capacity x 106 (kN.m)
0 300 600 900 1200 1500
Pre
dic
ted
ca
pa
city
x 1
06 (
kN
.m)
0
300
600
900
1200
1500
line of equality
Mean 0.985
SD 0.088
CV 0.089
b) ) 𝑟 = 0.25 Δ𝜀
M x 102 (kN.m)
0.0 0.5 1.0 1.5 2.0 2.5
P x 103 (kN)
0
1
2
3
4r = 1.0(peak points)
r = 0.0
r = 0.25
r = 0.50
r = 0.75
r = 1.0
14
Location of Critical Strain
x
y
h =
0.6 m
b = 0.6 m
Fire
( Left )
Fire
( Right )
Fire
( Top )
Fire
( Bottom )
c
cT x 10-3
-40 -30 -20 -10 0 10 20 30
y x 10-3
(m)
0
150
300
450
600
oT + tr cT max
x = 0.005
concrete crushing
z3 = 0.089 ,
z4 = -0.033
A
B
h
c = 0.226 m
b) 𝜀𝑐𝑇 dist. a) four-face heated
RC section c) concrete
forces
15
(9) Axial Capacity of Fire-Exposed RC Columns
x
y
h
b
Pr T
𝜀𝑐𝑇
y
𝑇𝑎𝑣𝑔 dist 𝑓𝑐𝑇 fcT
Cc
Temperature dependant
f ( Tavg )
100
200
300
400
500
600
700
800
900
305 mm3
05
mm
dy +
𝜀𝑠𝑡
16
Closed Form Solution for Standard Fire Exposure
Temperature Distribution
-600
-400
-200
0
200
400
600
800
1000
Tem
pe
ratu
re (
oC
)
305
mm
305 mmsteel bars
Fire (Bottom)
Fire (Upper)
Fire
(R
ight
)
Fire
(Lef
t)
Wickstrom’s Simple Method (1986)
Tavg 1Tavg 2
Tavg 1
x1
x2
Tavg 1Tavg 2
Tavg 1
x1
x2
x
y
z
zR 1L , B
R 20 , B
R 1R , B
R 1
L , 0
R 2
0 , 0
R 1
R , 0
R 1L , T
R 2
0 , T
R 1
R , T
z
T avg 1
Fire
( Left )
Fire
( Right )
Fire
( Top )
Fire
( Bottom )
area affectedby fire temp
area not affectedby fire temp
2
1
Line 1-1
Line 2-2
b
h
T avg 1T avg 2
T avg 1 T avg 1T avg 2
R 1L , B
R 20 , B
R 1R , B
R 1
L , 0
R 2
0 , 0
R 1
R , 0z
y
z
z
actual temp.
dist.
average
dist.
T avg
dist.
actual temp.
dist.
average
dist.
x
y
z
zR 1L , B
R 20 , B
R 1R , B
R 1
L , 0
R 2
0 , 0
R 1
R , 0
R 1L , T
R 2
0 , T
R 1
R , T
z
T avg 1
Fire
( Left )
Fire
( Right )
Fire
( Top )
Fire
( Bottom )
area affectedby fire temp
area not affectedby fire temp
2
1
Line 1-1
Line 2-2
b
h
T avg 1T avg 2
T avg 1 T avg 1T avg 2
R 1L , B
R 20 , B
R 1R , B
R 1
L , 0
R 2
0 , 0
R 1
R , 0z
y
z
z
actual temp.
dist.
average
dist.
T avg
dist.
actual temp.
dist.
average
dist.
Average Temperature
x
y
h
b
Pr T
𝜀𝑐𝑇
y
𝑇𝑎𝑣𝑔 dist
+
𝜀𝑠𝑡 𝑓𝑐𝑇 fcT
Cc
closed form solution
to evaluate fcT
Integration
Validation (33 columns)
Applied load x 103 (kN)
0 1 2 3 4
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0
1
2
3
4
line of equality
Lie and Wollerton [15]
Mean 1.117
SD 0.294
COV 0.263
Applied load x 103 (kN)
0.0 0.2 0.4 0.6 0.8 1.0
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0.0
0.2
0.4
0.6
0.8
1.0
Proposed method
line of equality
Hass [17]
Mean 0.877
SD 0.258
COV 0.295
Applied load x 103 (kN)
0.0 0.2 0.4 0.6 0.8 1.0 1.2 1.4
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0.0
0.2
0.4
0.6
0.8
1.0
1.2
1.4
line of equality
Dotreppe et al. [16]
Mean 0.782
SD 0.140
COV 0.179
a)
c)
b)
Applied load x 103 (kN)
0 1 2 3 4
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0
1
2
3
4
line of equality
Lie and Wollerton [15]
Mean 1.117
SD 0.294
COV 0.263
Applied load x 103 (kN)
0.0 0.2 0.4 0.6 0.8 1.0
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0.0
0.2
0.4
0.6
0.8
1.0
Proposed method
line of equality
Hass [17]
Mean 0.877
SD 0.258
COV 0.295
Applied load x 103 (kN)
0.0 0.2 0.4 0.6 0.8 1.0 1.2 1.4
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0.0
0.2
0.4
0.6
0.8
1.0
1.2
1.4
line of equality
Dotreppe et al. [16]
Mean 0.782
SD 0.140
COV 0.179
a)
c)
b)
Applied load x 103 (kN)
0 1 2 3 4
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0
1
2
3
4
line of equality
Lie and Wollerton [15]
Mean 1.117
SD 0.294
COV 0.263
Applied load x 103 (kN)
0.0 0.2 0.4 0.6 0.8 1.0
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0.0
0.2
0.4
0.6
0.8
1.0
Proposed method
line of equality
Hass [17]
Mean 0.877
SD 0.258
COV 0.295
Applied load x 103 (kN)
0.0 0.2 0.4 0.6 0.8 1.0 1.2 1.4
Pre
dic
ted
ca
pa
city x
10
3 (
kN
)
0.0
0.2
0.4
0.6
0.8
1.0
1.2
1.4
line of equality
Dotreppe et al. [16]
Mean 0.782
SD 0.140
COV 0.179
a)
c)
b)
20
(10) Validation RC Beams
Fire duration (min)
0 30 60 90 120 150
w* (
cm)
-120
-80
-40
0
Test Lin et al.
FEM - Kodur et al.
Sectional Analysis
Curvature x 10-3
(1/in)
0 1 2 3 4 5 6
Mom
ent (f
t.Ib
) x
10
10
0
2
4
6
8
10
12
Curvature x 10-6
(1/mm)
0 50 100 150 200 250
Mom
ent (k
N.m
)
0
40
80
120
160
Prior to Fire
1 hr fire exposure
6.10 m [20.01 ft]
20 kN
*w
0.75 m 1.50 m 1.50 m 0.75 m1.50 m
2#19
4#19
[4496 Ib]20 kN[4496 Ib]
20 kN[4496 Ib]
20 kN[4496 Ib]
[4.9 ft] [4.9 ft] [4.9 ft][2.5 ft] [2.5 ft]
i
21
Validation for RC Walls
0
10
20
30
40
50
60
70
80
90
100
0 10 20 30 40 50 60 70
Mid
-sp
an D
efle
ctio
n (m
m)
Time (min.)
Experimental Results -
Crozier and Sanjayan 2000
Calculated Results -
Sectional Analysis
22
Validation Restrained Beam
1.8 m
6.1 m
1.8 m
P2
1. Loaded prior to Fire test
2. P1 and P2 were 59 kN prior to fire
test.
3. During fire test, P1 and P2 varied
such that the cantilever deflection
stays constant.
1.8 m
6.1 m
1.8 m
P1
Δ
23
Fire duration (min)
0 60 120 180 240
Mid
-sp
an
de
fle
ctio
n (
mm
)
-250
-200
-150
-100
-50
0
Mid
-sp
an
de
fle
ctio
n (
in)
-8
-6
-4
-2
0
Test Lin et al. 5
Sectional Analysis
(3 iterations)
Fire duration (min)
0 60 120 180 240
Ca
ntile
ve
r lo
ad
s (
kN
)
0
30
60
90
120
Ca
ntile
ve
r lo
ad
s (
kip
s)
0
5
10
15
20
25
Test - P1 and P2
Sectional Analysis
(3 iterations)
P1
P2
Validation for a Frame
Axial load on column
= 1727 kN
P1 & P2= 78 & 49 kN
Δ1 and Δ2 were
monitored during
the fire test
Δ2 Δ1
24
P1
P2
Ball Bearing
Hinge
Roller
Support
150 mm Ceramic
Fiber Shielding
1750 2600 1400 1025
6775
10
50
13
10
28
60
50
0
FireFire
Fire
SEC 2-2
400 x 500
2-22 MM +
2-25 MM
FireFire
Fire
SEC 3-3
400 x 500
2-22 MM
FireFire
Fire
SEC 4-4
400 x 500
2-22 MM
Fire
Fire
SEC 1-1
500 x 500
Fire
11
11
2
2
4-22 MM 4-22 MM 4-22 MM
2000 3750 825
3
3
4
4
12-22 MM
150
150
50
50
DEFLECTION
mm
mm
SAP2000
Fang et al.
SCALE
P1
P2
(2012)
Fig. Error! No text of specified style in document.-1-Beam-column subassemblage
deformation after 𝟑 𝐡𝐫𝐬 ISO-834 fire exposure
𝜃 ∆2
∆1 (23% error)
I II III IV
P1
P2
V
VI 278181
47
101
142
P1
P2
91 15
110
38
53
P1
P2
187 166 6363
89
a) Primary BMD
c) Total BMD (Stiffnesses in 𝑁.𝑚𝑚2 )
b) Secondary BMD
13.50× 1012
137.60× 1012
16.50× 1012
3.47 × 1012
10.30× 1012
𝐸𝐼𝑒𝑓𝑓 =
8.26× 1012
I II III IV
P1
P2
V
VI 278181
47
101
142
P1
P2
91 15
110
38
53
P1
P2
187 166 6363
89
a) Primary BMD
c) Total BMD (Stiffnesses in 𝑁.𝑚𝑚2 )
b) Secondary BMD
13.50× 1012
137.60× 1012
16.50× 1012
3.47 × 1012
10.30× 1012
𝐸𝐼𝑒𝑓𝑓 =
8.26× 1012
(5% error)
(10% error)
25
Shear Capacity Validation
26
For additional details, please refer to:• Youssef MA, Diab M, EL-Fitiany SF, in-press, “Prediction of the Shear Capacity of
Reinforced Concrete Beams at Elevated Temperatures”, Magazine of ConcreteResearch.
• El-Fitiany SF, Youssef MA, 2014, “Interaction Diagrams for Fire-Exposed ReinforcedConcrete Sections”, Engineering Structures, 70: 246-259.
• El-Fitiany SF, Youssef MA, 2014, “Simplified Method to Analyze ContinuousReinforced Concrete Beams during Fire Exposure”, ACI Structural Journal, 111(1):145-155.
• El-Fitiany SF, Youssef MA, 2011, “Stress-Block Parameters for Reinforced ConcreteBeams during Fire Events”, ACI SP-279: Innovations in Fire Design of ConcreteStructures, Paper No. 1, pp. 1-39.
• El-Fitiany SF, Youssef MA, 2009, “Assessing the Flexural and Axial Behaviour ofReinforced Concrete Members at Elevated Temperatures using Sectional Analysis”,Fire Safety Journal, 44(5): 691-703.
• Youssef MA, El-Fitiany SF, Elfeki M, 2008, “Flexural Behavior of Protected ConcreteSlabs after Fire Exposure”, ACI SP-255: Designing Concrete Structures for FireSafety, Paper No. 3, pp. 47-74.
• Youssef MA and Moftah M, 2007, “General Stress-Strain Relationship for Concreteat Elevated Temperatures”, Engineering Structures, 29 (10): 2618-2634.
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