# Hydration Heat of Nonshrinkage Concrete in Large-Diameter CFST Arch Ribs Cured at Low Temperatures

Authors: Tuo Shi; Nianchun Deng; Dong Pan; Shi Wang
Journal: Advances in Civil Engineering
 (2020)

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## Abstract

To study the construction of concrete-filled steel tubular (CFST) arch bridges in Tibet, China, the hydration-temperature field of nonshrinkage concrete in large-diameter CFST arch ribs was evaluated in a temperature-testing box to simulate a low-temperature environment. A finite element simulation was then conducted to replicate the experimental results. Finally, an improved formula with the parameters related to the diameter, the position, and the retarding time of concrete for predicting the hydration heat generated by non-shrinkage concrete in large-diameter CFST arch ribs cured at low temperatures was proposed. The formula results were shown to be consistent with the experimental results for low-temperature conditions and large diameters. This research method can be extended to predict the hydration heat at all locations in different-diameter CFSTs with different concrete mixes cured at various temperatures.


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## Body

## 1. Introduction

Concrete-filled steel tubular (CFST) arch bridges can, under suitable conditions, be constructed for half the cost of a suspension bridge with the same span [1]. As a result, many CFST arch bridges have been built to carry highway and railway traffic in the past 20 years in China. At present, more than 400 CFST arch bridges have been built in country, and the longest spans are 530 and 575 m [2]. The pouring of concrete into steel tubes is key to constructing CFST arch bridges, and various high-performance concretes (e.g., nonshrinkage and self-compacting) have been applied [3].Hydration heat occurs during the curing of concrete and has been studied experimentally by many scholars. Zhou et al. [4] conducted experimental research and numerical simulations on the early hydration heat and stress in a concrete wall, showing that insulation measures were necessary during cold weather. A microsimulation of hydration heat under creep was carried out by Briffaut et al. [5], who determined that the rate of increase in the elastic stiffness and the tensile strength of ordinary concrete were reduced under higher hydration heat. Byard et al. [6] studied the hydration performance of concrete that included prewetted lightweight aggregate and found an increased degree of hydration. Zhou et al. [7] conducted hydration heat tests and finite element simulation analyses on a new impermeable concrete, determining that high or low ambient temperatures were not conducive to a reduction in the temperature difference caused by concrete hydration. Through experiments, Sedaghat et al. [8] established an empirical formula for the hydration heat of Portland cement cured at 23°C. Li et al. [9] studied the influence of nanoalumina and graphene oxide on the early hydration of cement. Their experimental research showed that both materials could increase the hydration heat of cement and accelerate the hydration process. Hu et al. [10] studied the effect of different functional agglomerations of carboxylic acid superplasticizer on the hydration heat of cement paste, showing that different functional units had different effects on the retarding time and peak hydration of the cement paste. Tan et al. [11] studied the effect of fly ash on the hydration of magnesium sulfate slurry using electrochemical impedance spectroscopy and confirmed the validity of this new research method through testing. Chorzepa et al. [12] established a multifactor hydration model simulation and carried out test verification, showing that the effect of the hydration model was significant. Chen and Xu [13] investigated the hydration-temperature field of three CFST members, observing that, after filling the steel tube with concrete, the cross section temperature of each member was higher than the ambient temperature. These results demonstrated that the temperature field was characterized by high inside and low outside temperatures. The maximum temperature difference between the inside and outside reached 8.5°C. Feng [14] conducted hydration-temperature field tests on circular and square CFST members showing that their cross section temperatures first increased and then decreased before finally approaching the atmospheric temperature. The temperature difference between the atmosphere and the square CFST members was greater than that between the atmosphere and the circular CFST members. Lin et al. [15, 16] tested a CFST arch having an outer diameter of 325 mm and a span of 10 m. The hydration temperature of the concrete in the test arch rib was similar to that of mass concrete; the temperature first increased and then decreased, and a temperature gradient was observed in the section. Xuan [17] observed that the temperature gradients and stresses observed in a CFST arch bridge having a 60 m span were likely caused by a higher hydration heat occurring when the arch-rib concrete was poured at low temperatures. Sun et al. [18] suggested that the thickness of the steel tube used in a CFST arch had less influence on the hydration-temperature field than did the diameter of the tube. Gao [19] conducted experiments and finite element analyses on CFST members and concluded that the outer surfaces of the CFST section were more affected by the ambient temperature than was the core over the first 7 days of hydration.Experts and scholars have thus explored the temperature field of hydration heat in CFST arch bridges, but the sizes and quantities of the test specimens in previous studies were too small to be applied to full-span bridges, the test conditions were not sufficiently controlled, and there was little research at low temperatures. Therefore, further research is urgently needed. With more CFST arch bridges currently being built for the Sichuan-Tibet Railway, it is important to study the hydration heat in large-diameter CFST arch ribs cured at low temperatures. This study addresses these gaps. The diameters of the CFST members tested in this study were sufficiently large to explore the temperature field of the hydration heat, and a temperature test box was employed to ensure specimen curing at consistently low temperatures. The results of this research were then used to reveal the law of hydration-heat temperature change of nonshrinkage concrete in large-diameter CFSTs cured at low temperatures and to predict the temperatures of different-diameter CFSTs at an early age at different locations using an empirical equation. This advancement could provide a helpful reference for the construction of CFST arch bridges in winter in Tibet.


## 2. Experimental Means and Methods

The experiments conducted in this study were designed to evaluate the development of the hydration-heat temperature field in 1.4 m and 1.6 m diameter CFST members in a temperature test box. The specific dimensions of the members are shown in Figures1 and 2 shows photos of the members. The mixing proportion of C55 nonshrinkage concrete used in the CFST members is shown in Table 1. The C55 concrete mix applied in this study was selected based on the results of a previous study showing good volume stability and mechanical properties of this mix in CFSTs cured at low temperature [20].Figure 1
Dimensions of the CFST members evaluated in this study (m). (a) 1.4 m diameter. (b) 1.6 m diameter.
(a)(b)Figure 2
Photos of the CFST members evaluated in this study. (a) 1.4 m diameter. (b) 1.6 m diameter. (c) Hard adiabatic foam.
(a)(b)(c)Table 1
Mixing proportion of C55 nonshrinkage concrete (kg/m3).
CementFly ashWater-reducing agentExpansive agentSandGravelWaterTotal4004512.9507111.0521572.427.9Because the influence of the CFST arch rib angle on the temperature field of the hydration heat could be ignored, the test pieces were oriented vertically in the temperature box to facilitate the placement of concrete. Four locating rings were welded within each steel tube, and high-strength insulated wire ropes were fixed to them across the test section to provide a lattice for attaching the temperature sensors (i.e., thermal resistors), as shown in Figure3. Note that a No.0 measuring point was also placed in the temperature test box to measure the ambient temperature. A wireless data acquisition system was used to acquire the temperature and stress data. The range of temperature sensors was from −30°C to +120°C, whose accuracy was 0.2°C.Figure 3
Layout of the measuring points.After the sensors were installed, the CFST members were placed in the temperature test box (Figure4), and the data acquisition system was connected. The temperature in the temperature test box was set to 0°C. The nonshrinkage concrete was then poured into the 1.4-m and 1.6-m diameter CFST members (Figure 5) at initial casting temperatures of 28 and 30°C, respectively. After casting was complete, the ends of the members were sealed with steel plates and insulation material to ensure that heat radiated from only the walls of the tubes. Finally, the temperature test box was closed. Data were then collected every 10 min starting from the beginning of pouring to obtain the temperature variation of the concrete during the process of hydration heat release. The testing was terminated after 7 days.Figure 4
Temperature test box.Figure 5
Change in hydration temperature in the CFST members over time when curing at 0°C. (a) 1.4-m diameter. (b) 1.6-m diameter. (c) Maximum temperature difference.
(a)(b)(c)


## 3. Results and Analysis

The hydration heats in the 1.4- and 1.6-m diameter CFST members exhibited consistent changes over time. The hydration temperatures of the concrete in the CFST members were centrosymmetric. Thus, only one quarter of the measured points (Nos. 1, 2, 3, and 4) and the ambient temperature (No. 0) were selected for data plotting and analysis. The temperatures of the concrete in the members rapidly reached their maximum after 20 h in the low-temperature test box (Figure5) and then decreased gradually until equalizing near the ambient temperature. As can be observed in Figure 5, the concrete near the edge of the steel tube was more affected by the low ambient temperature.The initial casting temperature of the 1.4-m diameter CFST member was 28°C, and its maximum temperature during hydration was 62.1°C, indicating a temperature increase of 34.1°C caused by hydration heat. The initial casting temperature of the 1.6-m diameter CFST member was 30°C, and its maximum temperature during hydration was 72.8°C, indicating a temperature increase of 42.8°C caused by hydration heat. Therefore, the larger-diameter CFST corresponded to a higher maximum hydration heat. The maximum difference in hydration heat measured within the 1.4- and 1.6-m diameter CFST members was 34.9 and 37.2°C, respectively. Thus, a larger-diameter CFST will exhibit a greater difference in temperature, owing to hydration heat. The hydration-heat characteristics of the CFST specimens were similar to those of mass concrete, suggesting that there was a greater temperature difference caused by the hydration heat of the CFST cured at low curing temperatures. Owing to the low curing temperature and the large difference in temperature caused by hydration heat, the cooling rate of the concrete was also large.A finite element analysis was conducted using ANSYS v.17.0 to further investigate the distribution of the hydration temperature of the nonshrinkage concrete in large-diameter CFST arch ribs. The PLANE77 element was selected to represent the concrete. The material parameters used in the finite element model are listed in Table2. The model was divided into 4.161 nodes and 1.360 elements. The hydration-heat model was based on the composite exponential formula, and its parameters were selected from the literature [21]. The formula is given as follows:(1)Qt=Q01−expmtn,where Qt is the cumulative hydration heat at time t at age t (d), Q0 is the final hydration heat, and m and n are coefficients of the rate of hydration heat.Table 2
Thermal parameters of the materials used in the finite element model.
MaterialDensity (kg/m3)Specific-heat capacity (kJ/m2 °C)Thermal conductivity (kJ/m2·h°C)Concrete2.4500.9810.09Steel7.8500.45199.124The axial length of the specimen was 1.5 m, and the diameters were 1.4 m and 1.6 m, respectively. In the test, two layers of heat preservation material were placed to cover both ends of the specimen to prevent heat escape. Therefore, the influence of the environment on the temperature field in the axial direction of the specimen could be ignored. Furthermore, because the temperature field of the CFST members was assumed to be uniform, the model was simplified as a 2D model. The boundary temperature of the 2D model was set to 0°C, and the heat-transfer coefficient was 4.99 W/m2 °C. The model mesh and selected measurement points are shown in Figure 6.Figure 6
Finite element model and measuring-point locations.As indicated by the comparisons in Figure7, the finite element analysis results agreed well with the experimental results: the heating and cooling sections of the hydration-heat curves were generally consistent, except during the initial concrete retarding phase. This result demonstrates that the finite element model established in the study was accurate, but that the composite exponential formula used to model the hydration heat could be improved for the early phase.Figure 7
Comparison of experimental and finite element simulation results for (a) 1.4 m and (b) 1.6-m diameter members.
(a)(b)At the retarding stage, too low ambient temperature would affect the hydration rate and prolong the retarding time of concrete, so the retarding time of edge concrete was longer than that of core concrete. At the retarding stage of edge concrete, the temperature of concrete would decrease due to the influence of low ambient temperature. The finite element simulation could not simulate the retarding stage, so there were differences at the retarding stage.


## 4. Discussion

### 4.1. Improved Hydration Heat Formula

An improved formula was developed in this study based on the experimental and finite element simulation results. The formula was built upon the work of Lee et al. [22] and Koo et al. [23], who previously improved the formula for predicting hydration temperature. The applicable condition for their formula is a constant temperature or the quasi-adiabatic condition, given as follows:(2)ΔTt=ΔTmax1−expatb,where ΔTt is the difference between the temperature of the concrete at age t (d) and its initial casting temperature, ΔTmax is the maximum increase in temperature, and a and b are coefficients of the rate of temperature change.As demonstrated by the early discrepancy in Figure8, the initial retarding time of the nonshrinkage concrete was not considered in this formula. Furthermore, formula (4) was only able to calculate the maximum temperature difference at the center of the section. Notably, the law describing the hydration temperature of concrete in a CFST is related to the CFST diameter, and there are some regularities in the temperature-field distribution of the concrete hydration heat at any location within. Therefore, an improved formula was developed as follows:(3)ΔTt=αDβrΔTmax1−expat−t0b,where αD is the diameter coefficient, defined as the ratio of the center temperature of the current-diameter CFST to the center temperature of a 1.5-m diameter CFST, βr is the location coefficient, defined as the ratio of the temperature at the current location to that at the core, and t0 is the retarding time of the concrete.Figure 8
Comparisons of the core temperature calculated by finite element analysis and formula (5) for a 1.5-m diameter CFST.The heating and cooling phases at the core of a 1.5-m diameter CFST were simulated to serve as benchmark data for formula (3). The maximum increase in temperature during the heating phase (ΔTmax1) was defined as the difference between the maximum temperature (Tmax) and the initial casting temperature (T1). Thus, ΔTmax1=Tmax−T1. The maximum decrease in temperature in the cooling phase (ΔTmax2) was defined as the difference between the maximum temperature (Tmax) and the ambient temperature (T0). Thus, ΔTmax2=Tmax−T0. The ambient temperature (T0) was 0°C, the initial casting temperature of the concrete T0 was 30°C, and the maximum temperature (Tmax) was 69°C. Therefore, the maximum temperature increase during the heating phase was ΔTmax1 = Tmax−T1 = 39.4°C. This value was fit according to formula (3) to obtain the coefficients, a1=−0.10 and b1=1.35. The maximum temperature decrease in the cooling phase was ΔTmax2 = 69.5°C. This value was fit according to formula (3) to obtain the coefficients, a2 = −7,875.4 and b2=−2.35. The calculated value obtained using the fitted formula (3) and the simulated values obtained from the finite element analysis were then compared and found to be similar, as shown in Figure 8.


### 4.2. Determination of ParameterαD

The parameter,αD (the ratio of the current-diameter CFST center temperature to the 1.5-m diameter CFST center temperature), in formula (3) was determined by the following method. First, CFST members having different diameters of 1.0, 1.2, 1.4, 1.6, 1.8, and 2.0 m were simulated using finite element software to obtain the center temperature curves of the shrinkage-free concrete, shown in Figure 9. Then, the different diameters were listed as abscissa coordinates, and the corresponding values of αD were taken as ordinate coordinates. The resulting points for the seven evaluated diameters are plotted in Figure 10, as is the fitted curve plotted using the Origin software. The following fitting formula was obtained by taking the maximum increase in temperature using the 1.5-m diameter CFST member as the benchmark, setting the diameter as the independent variable and αD as the dependent variable:(4)αD=−2.531×e−x/1.155+1.693.Figure 9
Center temperature curves of various finite element modeled CFST specimens.Figure 10
Fitted curve of parameterαD for different CFST diameters.


### 4.3. Determination of Parameterβr

The parameter,βr (the ratio of the temperature at the current location to that at the core), in formula (3) was determined by the following method. First, the 1.5-m diameter CFST member was simulated via finite element analysis, and the temperature curves of the nonshrinkage concrete were obtained at seven locations (0, R/6, R/3, R/2, 2 R/3, 5 R/6R, and R, where R is the radius of the tube), as shown in Figure 11. The resulting temperature curves are shown in Figure 12. Then, the ratios of the present locations to the radius of the CFST were taken as abscissa coordinates, and the ratios of the temperatures at each location to the center temperature were taken as ordinate coordinates, resulting in the seven points shown in Figure 13. The Origin software was then used to obtain the fitted curve through these points. Based on the center temperature of a 1.5-m diameter CFST, the distance from the center of the CFST was set as the independent variable and βr was set as the dependent variable, resulting in the following fitting formula:(5)βr=−0.205×ex/0.580+1.233.Figure 11
Measuring-point locations of the finite element model.Figure 12
Temperature curves of concrete at different locations.Figure 13
Fitted curve of parameterβr. Note. A comparison of formulas (4) and (5) indicates that the expressions for the CFST diameter parameter, αD, and the CFST location parameter, βr, are given in similar forms.


### 4.4. Discussion of the Application of the Proposed Formulas

The temperature curves of the 1.4- and 1.6-m diameter CFST members were calculated using formulas (3)–(5). The calculated curves, shown in Figures 14 and 15, can be observed to be consistent with the experimental results.Figure 14
Comparison of experimental and formula-calculated results for the 1.4-m diameter CFST member.Figure 15
Comparison of experimental and formula-calculated results for the 1.6-m diameter CFST member.Based on the results of finite element calculation, the formula proposed in this paper only prolonged the retarding time of concrete, and the temperature change of edge concrete (No.1 measuring point) at the retarding section was not considered. Therefore, the formula results at No.1 measuring point were different from the experimental results at the retarding stage of concrete.Furthermore, formulas (3)–(5) were applied using the data from three published studies [18, 19] to assess their consistency with the experimental results reported therein. The calculated curves, shown in Figures 16 and 17, can be observed to be consistent with the experimental results in the literature [18, 19].Figure 16
Comparison of formula-calculated results with the experimental results from Sun et al. [18].Figure 17
Comparison of formula-calculated results with the experimental results from Gao [19].The improved formulas proposed in this study are therefore able to adequately predict the hydration heat in large-diameter CFST at low temperatures.


## 4.1. Improved Hydration Heat Formula

An improved formula was developed in this study based on the experimental and finite element simulation results. The formula was built upon the work of Lee et al. [22] and Koo et al. [23], who previously improved the formula for predicting hydration temperature. The applicable condition for their formula is a constant temperature or the quasi-adiabatic condition, given as follows:(2)ΔTt=ΔTmax1−expatb,where ΔTt is the difference between the temperature of the concrete at age t (d) and its initial casting temperature, ΔTmax is the maximum increase in temperature, and a and b are coefficients of the rate of temperature change.As demonstrated by the early discrepancy in Figure8, the initial retarding time of the nonshrinkage concrete was not considered in this formula. Furthermore, formula (4) was only able to calculate the maximum temperature difference at the center of the section. Notably, the law describing the hydration temperature of concrete in a CFST is related to the CFST diameter, and there are some regularities in the temperature-field distribution of the concrete hydration heat at any location within. Therefore, an improved formula was developed as follows:(3)ΔTt=αDβrΔTmax1−expat−t0b,where αD is the diameter coefficient, defined as the ratio of the center temperature of the current-diameter CFST to the center temperature of a 1.5-m diameter CFST, βr is the location coefficient, defined as the ratio of the temperature at the current location to that at the core, and t0 is the retarding time of the concrete.Figure 8
Comparisons of the core temperature calculated by finite element analysis and formula (5) for a 1.5-m diameter CFST.The heating and cooling phases at the core of a 1.5-m diameter CFST were simulated to serve as benchmark data for formula (3). The maximum increase in temperature during the heating phase (ΔTmax1) was defined as the difference between the maximum temperature (Tmax) and the initial casting temperature (T1). Thus, ΔTmax1=Tmax−T1. The maximum decrease in temperature in the cooling phase (ΔTmax2) was defined as the difference between the maximum temperature (Tmax) and the ambient temperature (T0). Thus, ΔTmax2=Tmax−T0. The ambient temperature (T0) was 0°C, the initial casting temperature of the concrete T0 was 30°C, and the maximum temperature (Tmax) was 69°C. Therefore, the maximum temperature increase during the heating phase was ΔTmax1 = Tmax−T1 = 39.4°C. This value was fit according to formula (3) to obtain the coefficients, a1=−0.10 and b1=1.35. The maximum temperature decrease in the cooling phase was ΔTmax2 = 69.5°C. This value was fit according to formula (3) to obtain the coefficients, a2 = −7,875.4 and b2=−2.35. The calculated value obtained using the fitted formula (3) and the simulated values obtained from the finite element analysis were then compared and found to be similar, as shown in Figure 8.


## 4.2. Determination of ParameterαD

The parameter,αD (the ratio of the current-diameter CFST center temperature to the 1.5-m diameter CFST center temperature), in formula (3) was determined by the following method. First, CFST members having different diameters of 1.0, 1.2, 1.4, 1.6, 1.8, and 2.0 m were simulated using finite element software to obtain the center temperature curves of the shrinkage-free concrete, shown in Figure 9. Then, the different diameters were listed as abscissa coordinates, and the corresponding values of αD were taken as ordinate coordinates. The resulting points for the seven evaluated diameters are plotted in Figure 10, as is the fitted curve plotted using the Origin software. The following fitting formula was obtained by taking the maximum increase in temperature using the 1.5-m diameter CFST member as the benchmark, setting the diameter as the independent variable and αD as the dependent variable:(4)αD=−2.531×e−x/1.155+1.693.Figure 9
Center temperature curves of various finite element modeled CFST specimens.Figure 10
Fitted curve of parameterαD for different CFST diameters.


## 4.3. Determination of Parameterβr

The parameter,βr (the ratio of the temperature at the current location to that at the core), in formula (3) was determined by the following method. First, the 1.5-m diameter CFST member was simulated via finite element analysis, and the temperature curves of the nonshrinkage concrete were obtained at seven locations (0, R/6, R/3, R/2, 2 R/3, 5 R/6R, and R, where R is the radius of the tube), as shown in Figure 11. The resulting temperature curves are shown in Figure 12. Then, the ratios of the present locations to the radius of the CFST were taken as abscissa coordinates, and the ratios of the temperatures at each location to the center temperature were taken as ordinate coordinates, resulting in the seven points shown in Figure 13. The Origin software was then used to obtain the fitted curve through these points. Based on the center temperature of a 1.5-m diameter CFST, the distance from the center of the CFST was set as the independent variable and βr was set as the dependent variable, resulting in the following fitting formula:(5)βr=−0.205×ex/0.580+1.233.Figure 11
Measuring-point locations of the finite element model.Figure 12
Temperature curves of concrete at different locations.Figure 13
Fitted curve of parameterβr. Note. A comparison of formulas (4) and (5) indicates that the expressions for the CFST diameter parameter, αD, and the CFST location parameter, βr, are given in similar forms.


## 4.4. Discussion of the Application of the Proposed Formulas

The temperature curves of the 1.4- and 1.6-m diameter CFST members were calculated using formulas (3)–(5). The calculated curves, shown in Figures 14 and 15, can be observed to be consistent with the experimental results.Figure 14
Comparison of experimental and formula-calculated results for the 1.4-m diameter CFST member.Figure 15
Comparison of experimental and formula-calculated results for the 1.6-m diameter CFST member.Based on the results of finite element calculation, the formula proposed in this paper only prolonged the retarding time of concrete, and the temperature change of edge concrete (No.1 measuring point) at the retarding section was not considered. Therefore, the formula results at No.1 measuring point were different from the experimental results at the retarding stage of concrete.Furthermore, formulas (3)–(5) were applied using the data from three published studies [18, 19] to assess their consistency with the experimental results reported therein. The calculated curves, shown in Figures 16 and 17, can be observed to be consistent with the experimental results in the literature [18, 19].Figure 16
Comparison of formula-calculated results with the experimental results from Sun et al. [18].Figure 17
Comparison of formula-calculated results with the experimental results from Gao [19].The improved formulas proposed in this study are therefore able to adequately predict the hydration heat in large-diameter CFST at low temperatures.


## 5. Conclusion

A series of CFST specimens were subjected to curing in a 0°C temperature-controlled room to observe the relationship between hydration heat and curing time according to the diameter of and location within the CFST specimens. The hydration-heat characteristics of CFST were observed to be similar to mass concrete, suggesting that there was a greater temperature difference caused by CFST hydration heat when cured at low temperatures. Owing to the low curing temperature and large temperature difference caused by hydration heat, the cooling rate of concrete was large.A finite element model of hydration heat was then established, and its behavior was compared with the experimental results. The observed differences were then used to derive an improved formula for predicting the change in hydration heat according to CSFT parameters. The improved formulas proposed in this study were demonstrated to effectively predict the law of hydration heat in large-diameter nonshrinkage CFST arch ribs at low temperatures of about 0°C.Although limited to a single type of concrete in a small variety of CFST specimens cured at 0°C in this study, the research method applied can be extended to predict the hydration heat at many different locations in many different-diameter CFSTs cured at different temperatures with various concrete-mix proportions.



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