Fire Resistance and Seismic Performance Study of a High-Strength Construction Steel Using Creep and Internal Friction Analysis

Fire resistance and seismic performance are the two of the most important considerations for the design of construction steel. The fire resistance of the high-strength construction steel, Q460FRE, which contains low Mo, was investigated by means of creep test under different experiment conditions. Then, the seismic performance of the Q460FRE steel, after being subjected to various fire temperatures, was characterized by internal friction analysis. The Q460FRE steel exhibited excellent fire resistance, and the yield strength at 600 °C was 67.4% of the yield strength at room temperature. The constitutive equation of creep stress and fracture time at 600 °C was established. The bearing tensile stress of the Q460FRE steel should be lower than 337 MPa to ensure at least 1 h to evacuate from the fire. The creep stress and alternating temperature significantly affected the serration behavior of the creep strain. The internal friction analysis indicated that the seismic performance of the Q460FRE steel decreased with the increase in fire temperature, being consistent with the analysis results of the seismic performance characterized by the yield ratio.


Introduction
With the rapid development of the construction industry, higher requirements have been put forward for the strength, service life and safety of construction steel. Natural disasters such as earthquake and fire would cause devastating damage to buildings. Therefore, fire resistance and seismic performance are the two major problems that need to be solved urgently for building steel. Meanwhile, low cost and green environmental protection have become the development direction of construction steel in order to achieve the purpose of low carbon economy: saving raw materials and energy, as well as reducing emissions.
In general, the yield strength of conventional structural steels at 600 • C will drop to less than 50% of the yield strength at room temperature, thus losing their bearing capacity [1][2][3]. Although fire-resistant coating can improve the fire resistance of steel structure, it will add to the manufacturing cost and pollute the environment [4,5]. Therefore, improving the fire resistance of steel itself is the most effective approach to increase the fire resistance capacity of buildings. The main idea of alloying traditional fire-resistant steel is to add a high molybdenum (exceeds 0.5 wt.%) and improve the high-temperature performance of steel by the solid solution and precipitation strengthening of Mo [6]. However, the high content of Mo significantly increases the cost of the alloy. In recent years, the composite microalloying of Nb, V, Ti and low Mo ( 0.3%) has provided a feasible and economical means for the design of fire-resistant steel [7][8][9]. A high-strength fire-resistant construction steel Q460FRE containing high (Nb+Ti) and low Mo microalloying was developed. In the Metals 2021, 11, 1045 2 of 14 case of fire, the yield strength of fire-resistant steel at 600 • C should reach more than 2/3 of the yield strength at room temperature [10,11]. Previous investigations have focused on the microstructure and tensile properties of fire-resistant steel at elevated temperature [12][13][14]. Unfortunately, their creep behavior, which can serve as a significant standard to evaluate reliability and safety under high temperature and load conditions [15,16], has not been studied systematically thus far.
The design of fire-resistant steel should also consider the seismic performance to avoid catastrophic earthquake damage to the steel structure. The seismic performance of steel is usually characterized by the yield ratio [17]. A low yield ratio means that steel can produce plastic deformation in a wide range, thus absorbing seismic energy and improving the seismic performance of steel structures [18]. In addition, internal friction represents the damping capacity of material against vibration, and it is related to atomic and magnetic rearrangements within the material [19]. The higher the internal friction value, the vibration energy consumption capacity of the steel itself, generating better seismic performance [20].
In this study, the fire resistance and seismic performance of a high-strength construction steel Q460FRE were investigated using creep and internal friction test. In order to study the fire resistance of the Q460FRE steel, the Gleeble-3500 thermal simulation testing machine (DSI, St. Paul, MN, USA) was used to evaluate the effect of constant load at 600 • C and alternating temperature on the creep behavior. Then, the internal friction test was carried out after the steel held at 250 • C to 600 • C for 1 h to analyze the seismic performance of the steel after a fire. Moreover, the relationship between internal friction value and yield ratio was discussed.

Test Steel
All test specimens were cut from a thermo-mechanically controlled processed (TMCP) Q460FRE steel sheet with a thickness of 20 mm. The chemical composition of the Q460FRE steel was analyzed by X-ray fluorescence spectrometer (BRUKER D8 Advance, Karlsruhe, Germany), as shown in Table 1. The microstructures of the Q460FRE steel composed of ferrite, bainite and martensite-austenite (MA) constituent are shown in Figure 1. Bainite is beneficial to increase the strength of the Q460FRE steel.

Microstructural Characterizations
The microstructures of the specimens were characterized by a field-emission scanning electron microscope (FESEM, Tescan MIRA3 XMU, Brno, Czech Republic). Speci-

Microstructural Characterizations
The microstructures of the specimens were characterized by a field-emission scanning electron microscope (FESEM, Tescan MIRA3 XMU, Brno, Czech Republic). Specimens for FESEM were prepared by mechanical polishing and following by eroded with 4% nitric acid alcohol.

Creep Test
Cylindrical bar tensile specimens with a gauge length of 40 mm and a diameter of 6 mm ( Figure 2) were used in this study. The constant load creep test was carried out with a Gleeble-3500 thermal simulation testing machine at 600 • C in a vacuum (the vacuum value was 0.1 Pa), as shown in Figure 3. The constant tensile stress values were 184 MPa, 210 MPa, 263 MPa and 316 MPa, respectively. The fracture morphology of the tensile specimens was observed by a FESEM.
The microstructures of the specimens were characterized by a field-emissio ning electron microscope (FESEM, Tescan MIRA3 XMU, Brno, Czech Republic) mens for FESEM were prepared by mechanical polishing and following by erod 4% nitric acid alcohol.

Creep Test
Cylindrical bar tensile specimens with a gauge length of 40 mm and a diame mm ( Figure 2) were used in this study. The constant load creep test was carried o a Gleeble-3500 thermal simulation testing machine at 600 °C in a vacuum (the v value was 0.1 Pa), as shown in Figure 3. The constant tensile stress values were 18 210 MPa, 263 MPa and 316 MPa, respectively. The fracture morphology of the tensi imens was observed by a FESEM.
The constant stress (263 MPa) creep test under heating and cooling cycles was out to evaluate the deformation behavior of steel at alternating temperature. The t ature varied between 200 °C and 600 °C, with a heating rate and a cooling rate of 2 and 10 °C/s, respectively.

Internal Friction Test
The internal friction (IF) test was conducted on an MFP-1000 multifunctional friction apparatus (Hefei, China) to analyze the seismic performance of the Q460F after a fire. After holding in the 250-600 °C temperature range for 1 h, the IF sp were processed into 70 mm × 1.8 mm × 1.2 mm by wire cutting and then mech polished with 1200 grit emery paper.

Tensile Properties
The typical engineering stress-engineering strain curves of the Q460FRE ste room temperature (25°C) and 600 °C are depicted in Figure 4. It shows that the of the Q460FRE steel decreased with the increase in temperature, while the elo underwent an increase as the temperature raised. When the temperature of the ten The constant stress (263 MPa) creep test under heating and cooling cycles was carried out to evaluate the deformation behavior of steel at alternating temperature. The temperature varied between 200 • C and 600 • C, with a heating rate and a cooling rate of 28.6 • C/s and 10 • C/s, respectively.

Internal Friction Test
The internal friction (IF) test was conducted on an MFP-1000 multifunctional internal friction apparatus (Hefei, China) to analyze the seismic performance of the Q460FRE steel after a fire. After holding in the 250-600 • C temperature range for 1 h, the IF specimens were processed into 70 mm × 1.8 mm × 1.2 mm by wire cutting and then mechanically polished with 1200 grit emery paper.

Tensile Properties
The typical engineering stress-engineering strain curves of the Q460FRE steel under room temperature (25 • C) and 600 • C are depicted in Figure 4. It shows that the strength of the Q460FRE steel decreased with the increase in temperature, while the elongation underwent an increase as the temperature raised. When the temperature of the tensile test increased from 25 • C and 600 • C, the yield strength decreased from 463 MPa to 312 MPa, with a decrease of 32.6%. Moreover, the elongation increased from 22.2% to 45.6%, with an increase of up to 105%. The decrease in strength at elevated temperature is related to the following factors [21]: (1) the movement of dislocations (slip and climb) leads to the occurrence of plastic deformation; (2) the growth of grain and coarsening of carbide precipitated phase lead to the dislocation easier to move; (3) grain boundary sliding. Particularly, when the drawing temperature rises above 400 • C, flow stress reduces dramatically, leading to a sharp decline in strength [22].

Evaluation of the Fire Resistance Utilizing Creep Test
The creep strain evolution during various uniaxial tensile stress creep tests at is plotted in Figure 5. When the creep stress was less than 263 MPa, the specimen not fractured after the 2 h creep test. The creep strain that occurred increased from to 2.27%, with the creep stress increasing from 184 MPa to 263 MPa. The creep strai curves presented two obvious stages [24]. In the primary creep stage, the creep str creased sharply, which was defined as the transient creep stage. Then, the creep fluctuated within a small range during the steady creep stage. When the creep stre to 316 MPa, the creep curve presented a third stage: accelerated creep, during wh creep strain rate increased sharply until the specimen fractures, as shown in Figu The specimen suddenly fractured after about 74 min of stretching. In a previous study, the yield strength of the conventional structural steel and the fire-resistant steel was 495 MPa and 544 MPa, respectively, at room temperature, and their yield strength dropped to 204 MPa and 287 MPa, respectively at 600 • C [2]. In this work, compared with the room temperature tensile, the yield strength decreased by less than one third at 600 • C, which indicated that the tensile properties of the Q460FRE steel complied with the design requirements of fire-resistant steel. Nanoscale carbide particles were not easy to precipitate during the TMCP process. However, large amounts of nanoscale carbide particles precipitated at elevated temperature, which played a good role in precipitation strengthening, thus significantly improving the high-temperature strength of fire-resistant steel [23].

Evaluation of the Fire Resistance Utilizing Creep Test
The creep strain evolution during various uniaxial tensile stress creep tests at 600 • C is plotted in Figure 5. When the creep stress was less than 263 MPa, the specimens have not fractured after the 2 h creep test. The creep strain that occurred increased from 0.20% to 2.27%, with the creep stress increasing from 184 MPa to 263 MPa. The creep strain-time curves presented two obvious stages [24]. In the primary creep stage, the creep strain increased sharply, which was defined as the transient creep stage. Then, the creep strain fluctuated within a small range during the steady creep stage. When the creep stress rose to 316 MPa, the creep curve presented a third stage: accelerated creep, during which the creep strain rate increased sharply until the specimen fractures, as shown in Figure 5d. The specimen suddenly fractured after about 74 min of stretching. curves presented two obvious stages [24]. In the primary creep stage, the creep strain in creased sharply, which was defined as the transient creep stage. Then, the creep strain fluctuated within a small range during the steady creep stage. When the creep stress rose to 316 MPa, the creep curve presented a third stage: accelerated creep, during which the creep strain rate increased sharply until the specimen fractures, as shown in Figure 5d The specimen suddenly fractured after about 74 min of stretching.  Normally, the creep displacement-holding time curve could be fitted by an empirical fitting equation [25,26]: where h 0 denotes the displacement at the beginning stage of the creep, and a, b and k are fitting constants. In this study, the relationship between creep strain and time during the steady-state creep stage could be fitted according to the following formula: where ε 0 and t 0 refer to the creep strain and time at the beginning of the steady-state creep stage. In general, at a certain temperature, the relationship between the steady-state creep strain rate ( . ε) and the creep stress can be expressed by the following formula [27]: where A is a constant related to material properties and temperature; n refers to the stress index of steady-state creep. Based on the experimental data of creep test, Figure 6a presents the function relation between . ε and σ, and the equation of the regression line is as follows: ln . ε m = 6.26 ln σ − 48.92 (4) Figure 6b presents the variation of the ln-ln plots of tr vs. σ. Usually, fire-resistant steel needs to be carried for 1-3 h in a fire without breaking, to ensure that personnel have enough time to escape. It can be calculated that the critical creep stresses of the Q460FRE steel for tr = 1 h and tr = 2 h at 600 °C were 337 MPa and 282 MPa, respectively, i.e., 72.8% and 60.9% of the yield strength at room temperature. It can be concluded that the steady-state creep stress index (n) of Q460FRE was 6.26. The n is widely used to analyze the creep deformation mechanism [28]: n = 1 corresponding to diffusion creep; n = 2 for grain boundary sliding; n = 3-8 for dislocation glide or climb mechanism. It indicates that the creep deformation of the Q460FRE steel was controlled by dislocation motion at 600 • C.
The creep fracture time (t r ) can be derived according to Monkman-Grant's mathematical equation [29]: where C is a material constant independent of creep stress and temperature and m is a constant approximately equal to 1. In this study, the value of ε and σ can be described as: ln t r = −6.26 ln σ + 36.42 (6) Figure 6b presents the variation of the ln-ln plots of t r vs. σ. Usually, fire-resistant steel needs to be carried for 1-3 h in a fire without breaking, to ensure that personnel have enough time to escape. It can be calculated that the critical creep stresses of the Q460FRE steel for t r = 1 h and t r = 2 h at 600 • C were 337 MPa and 282 MPa, respectively, i.e., 72.8% and 60.9% of the yield strength at room temperature.
It is found that the creep stress significantly affects the serration behavior of the creep strain during the secondary creep stage. When the creep stress increased from 184 MPa to 263 MPa, the fluctuation period of the creep strain showed a prolonged trend. When the stress was less than 210 MPa, the creep strain had eleven peak values, and the creep strain had six peak values under the creep stress of 263 MPa. When creep stress increased to 316 MPa, no obvious serration shape was observed. Figure 7 shows the curve of creep strain peak interval evolution under the creep stress of 184 MPa. It illustrates that the strain peak interval was between 850 s and 600 s. The strain peak interval decreased with creep time, and the rate of decline gradually slowed down.
The serration behavior is related to the dislocation-solute interactions and dislocationprecipitate interactions [30]. Dislocations distort the lattice, causing an elastic stress field that acts on nearby solute atoms. When a movable dislocation is being blocked, a solute cloud possibly forms around it, and the movable dislocation is fastened. Nano-scale precipitates in the steel can also pin dislocation [31]. Under the action of external stress, dislocation may overcome these obstacles by thermally activated motion. Moreover, in low-carbon steels, the interstitial atoms (C and N) distributed near the core of dislocations could release the lattice distortion or atomic-level stress. Thereby, the serration behavior was derived from the repeated action of the moving dislocations, were pinned by diffusing solutes and precipitates, and then broke free from this pinning. strain during the secondary creep stage. When the creep stress increased from 263 MPa, the fluctuation period of the creep strain showed a prolonged trend stress was less than 210 MPa, the creep strain had eleven peak values, and the c had six peak values under the creep stress of 263 MPa. When creep stress incre MPa, no obvious serration shape was observed. Figure 7 shows the curve of c peak interval evolution under the creep stress of 184 MPa. It illustrates that the interval was between 850 s and 600 s. The strain peak interval decreased with and the rate of decline gradually slowed down. The serration behavior is related to the dislocation-solute interactions a tion-precipitate interactions [30]. Dislocations distort the lattice, causing an el field that acts on nearby solute atoms. When a movable dislocation is being solute cloud possibly forms around it, and the movable dislocation is fastened. precipitates in the steel can also pin dislocation [31]. Under the action of exte dislocation may overcome these obstacles by thermally activated motion. M low-carbon steels, the interstitial atoms (C and N) distributed near the core of d could release the lattice distortion or atomic-level stress. Thereby, the serratio was derived from the repeated action of the moving dislocations, were pinned ing solutes and precipitates, and then broke free from this pinning.
The microstructure type of the Q460FRE steel did not change after the cre composed of ferrite, bainite and MA constituent, as shown in Figure 8. How pared with the TMCP specimen, the MA constituent in creep specimens decom became finer, as denoted by the red arrow. The smaller the creep stress, the M ent has enough time to decompose, resulting in the finer MA constituent. In microalloying strong carbide-forming elements (Nb and Ti) were mainly diss ferrite and bainite at room temperature, and the strengthening effect was com small. The C obtained by the decomposition of the MA constituent could be with Mo, Nb and Ti to generate dispersed particles at elevated temperature [ fore, nano-scale carbide particles precipitated during creep experiments at 60 could enlarge the dislocation pinning and the grain boundary effects, being co improving the strength of steel at high temperature. The microstructure type of the Q460FRE steel did not change after the creep test, still composed of ferrite, bainite and MA constituent, as shown in Figure 8. However, compared with the TMCP specimen, the MA constituent in creep specimens decomposed and became finer, as denoted by the red arrow. The smaller the creep stress, the MA constituent has enough time to decompose, resulting in the finer MA constituent. In addition, microalloying strong carbide-forming elements (Nb and Ti) were mainly dissolved into ferrite and bainite at room temperature, and the strengthening effect was comparatively small. The C obtained by the decomposition of the MA constituent could be combined with Mo, Nb and Ti to generate dispersed particles at elevated temperature [23]. Therefore, nano-scale carbide particles precipitated during creep experiments at 600 • C. They could enlarge the dislocation pinning and the grain boundary effects, being conducive to improving the strength of steel at high temperature.
With the increase in time, the number of nano-scale particles that precipitated increased first and then became stable. Plenty of nano-scale particles provided high-density sites to form dislocation pile-up. The period of the dislocation pile-up formation/relaxation became shorter under a constant external loading [32]. Therefore, the strain peak interval decreased with creep time under the creep stress of 184 MPa. As the applied stress increased, more time was needed to generate sufficient dislocation pile-up to offset the applied stress, resulting in a longer peak interval. When the applied stress increased to a certain value, the interaction effect between dislocation and solute or dislocation and precipitate was not sufficiently grave to cause the serration behavior. Figure 9 shows the macroscopic morphology and fracture morphology of the specimen after the creep test under the stress of 316 MPa at 600 • C. There was obvious necking at the fracture, which was consistent with the tensile curve. The fracture surface was dominated by deep dimples, which was typical microvoid coalescence ductile fracture being formed through the nucleation, growth, and coalescence of microvoids [33]. With the increase in time, the number of nano-scale particles that precipitated increased first and then became stable. Plenty of nano-scale particles provided high-density sites to form dislocation pile-up. The period of the dislocation pile-up formation/relaxation became shorter under a constant external loading [32]. Therefore, the strain peak interval decreased with creep time under the creep stress of 184 MPa. As the applied stress increased, more time was needed to generate sufficient dislocation pile-up to offset the applied stress, resulting in a longer peak interval. When the applied stress increased to a certain value, the interaction effect between dislocation and solute or dislocation and precipitate was not sufficiently grave to cause the serration behavior. Figure 9 shows the macroscopic morphology and fracture morphology of the specimen after the creep test under the stress of 316 MPa at 600 °C. There was obvious necking at the fracture, which was consistent with the tensile curve. The fracture surface was dominated by deep dimples, which was typical microvoid coalescence ductile fracture being formed through the nucleation, growth, and coalescence of microvoids [33].

Effect of Alternating Temperature on the Creep Behavior
In order to simulate the effect of alternating fire temperature on the tensile properties of the Q460FRE steel, the creep experiments under heating and cooling cycles were carried out. The temperature varied between 600 °C and 200 °C, with a constant loading stress of

Effect of Alternating Temperature on the Creep Behavior
In order to simulate the effect of alternating fire temperature on the tensile properties of the Q460FRE steel, the creep experiments under heating and cooling cycles were carried out. The temperature varied between 600 • C and 200 • C, with a constant loading stress of 263 MPa, and a total of 120 heating and cooling cycles were undertaken in two hours. Due to the effect of thermal expansion and cold contraction, the creep strain of the specimen kept the same trend with the temperature, as shown in Figure 10. The specimen shrinks when cooled and elongates when heated. However, with the increase in creep time, the effect of cooling shrinkage was gradually weakened, and the creep strain increased. After two hours' creep test, the strain reached 0.31%. Compared with the creep test at the constant temperature of 600 • C, the creep strain was reduced by 87.3%.

Effect of Alternating Temperature on the Creep Behavior
In order to simulate the effect of alternating fire temperature on the tensile properties of the Q460FRE steel, the creep experiments under heating and cooling cycles were carried out. The temperature varied between 600 °C and 200 °C, with a constant loading stress o 263 MPa, and a total of 120 heating and cooling cycles were undertaken in two hours. Due to the effect of thermal expansion and cold contraction, the creep strain of the specimen kept the same trend with the temperature, as shown in Figure 10. The specimen shrinks when cooled and elongates when heated. However, with the increase in creep time, the effect of cooling shrinkage was gradually weakened, and the creep strain increased. Afte two hours' creep test, the strain reached 0.31%. Compared with the creep test at the con stant temperature of 600 °C, the creep strain was reduced by 87.3%.

Seismic Performance Characterized by the Internal Friction Analysis
Internal friction-temperature spectra of the Q460FRE steel with different treated states are shown in Figure 11. The measurement spectra are composed of the background IF and the Snoek-Ke-Koster (SKK) peak [34]. With the increase in fire temperature, both the background IF and the SKK peak reduced gradually, showing a strong consistency The result indicates that the damping capacity of the Q460FRE steel decreased gradually with the increase in fire temperature. The damping capacity of the steel was attributed to

Seismic Performance Characterized by the Internal Friction Analysis
Internal friction-temperature spectra of the Q460FRE steel with different treated states are shown in Figure 11. The measurement spectra are composed of the background IF and the Snoek-Ke-Koster (SKK) peak [34]. With the increase in fire temperature, both the background IF and the SKK peak reduced gradually, showing a strong consistency. The result indicates that the damping capacity of the Q460FRE steel decreased gradually with the increase in fire temperature. The damping capacity of the steel was attributed to the amount of the grain-boundary precipitates, i.e., the less the precipitates, the higher the damping capacity [35].
The mechanism of the SKK peak was related to the interaction between interstitial carbon atoms and dislocation [36]. After simulating the fire process, interstitial carbon atoms and micro-alloy elements in steel were precipitated in the form of carbide, and the higher the temperature, the more precipitates. Figure 12 shows that the microstructures of the Q460FRE steel still composed of ferrite, bainite and MA constituent after holding at different temperature for 1 h. The ferrite grain boundaries were clearly visible. However, M/A components were gradually decomposed and refined with the increase in holding temperature, as denoted by the red arrows. During the heating process, the carbon enriched in the M/A components could rapidly diffuse to the surrounding carbon-poor ferrite matrix and combined with Mo, Nb and Ti to generate carbide precipitation at high temperature, leading to the gradual decomposition of M/A components [23,37]. The higher the temperature, the greater the diffusion driving force of carbon atoms, the more significant the decomposition of M/A components. Therefore, the carbon soluble in the matrix was reduced, leading to the decrease in the internal friction of the steel.

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the amount of the grain-boundary precipitates, i.e., the less the precipitates, the higher the damping capacity [35]. The mechanism of the SKK peak was related to the interaction between interstitial carbon atoms and dislocation [36]. After simulating the fire process, interstitial carbon atoms and micro-alloy elements in steel were precipitated in the form of carbide, and the higher the temperature, the more precipitates. Figure 12 shows that the microstructures of the Q460FRE steel still composed of ferrite, bainite and MA constituent after holding at different temperature for 1 h. The ferrite grain boundaries were clearly visible. However, M/A components were gradually decomposed and refined with the increase in holding temperature, as denoted by the red arrows. During the heating process, the carbon enriched in the M/A components could rapidly diffuse to the surrounding carbon-poor fer- Compared with the measured values of the Q460FRE steel, the variation law of the seismic performance obtained from the internal friction test was consistent with that obtained from the yield ratio. As seen from Figure 13a and Table 2, with the increase in fire temperature, the internal friction of the Q460FRE steel at room temperature decreased continuously, and the yield ratio increased as a whole. Figure 13b shows the relationship between the IF value and the yield ratio of the Q460FRE seismic fire-resistant steel at room temperature. There was a linear relationship between the IF value and the yield ratio, indicating that it was feasible to use internal friction to characterize the seismic performance of steel. It requires the yield ratio of anti-seismic construction steel to be less than 0.85 [38], so the corresponding background IF value should be higher than 3.1 × 10 -4 .  Compared with the measured values of the Q460FRE steel, the variation law of the seismic performance obtained from the internal friction test was consistent with that obtained from the yield ratio. As seen from Figure 13a and Table 2, with the increase in fire temperature, the internal friction of the Q460FRE steel at room temperature decreased continuously, and the yield ratio increased as a whole. Figure 13b shows the relationship between the IF value and the yield ratio of the Q460FRE seismic fire-resistant steel at room temperature. There was a linear relationship between the IF value and the yield ratio, indicating that it was feasible to use internal friction to characterize the seismic performance of steel. It requires the yield ratio of anti-seismic construction steel to be less than 0.85 [38], so the corresponding background IF value should be higher than 3.1 × 10 −4 .

Conclusions
In this work, the fire resistance and seismic performance of a high-strength construction steel Q460FRE were investigated by creep and internal friction test. The following conclusions were obtained: (1) The Q460FRE steel exhibited better fire resistance than conventional structural steel, and the yield strength at 600 °C was 67.4% of the yield strength at room temperature.
(2) The constitutive equation of creep stress and fracture time at 600 °C was established. The bearing tensile stress of the Q460FRE steel should be lower than 337 MPa to ensure at least 1 hour of evacuation time. The serration behavior of the creep strain was related to the dislocation-solute interactions and dislocation-precipitate interactions.
(3) Due to the effect of thermal expansion and cold contraction, the creep strain increased with fluctuation at alternating temperature and was lower than that of the creep test at the constant temperature of 600 °C.
(4) An internal friction test could be used well to evaluate the seismic performance of steel. The damping capacity of the Q460FRE steel decreased with the increase in fire temperature, which was consistent with the analysis results of the seismic performance characterized by the yield ratio.