Experimental and Theoretical Investigation on the Thermo-Mechanical Properties of Recycled Aggregate Concrete Containing Recycled Rubber

Introduction

In recent years, an enormous number of buildings, pavements, and bridges have expired out of service life with the improvement of urbanization, causing the amount of waste concrete to increase rapidly. Consequently, the construction industry has been committed to the development of sustainable resources, focusing on innovations and using recycled materials for limited natural aggregates. The common construction waste is mainly waste concrete and masonry materials that can be converted into recycled aggregates (RAs) with a particular program treatment and can be utilized to replace some of natural aggregates (NAs) to produce recycled aggregate concrete (RAC) (Tang et al., 2018; Xiao et al., 2018; Tang et al., 2019; Tang et al., 2020; Xiong et al., 2020). The use of RA can not only alleviate the current situation of natural resources (Ahmed and Lim, 2021) but also reduce environmental pollution, CO2 emissions, and land occupation resulting from a large amount of construction waste (Arulrajah et al., 2015).

Most studies on RAC have focused on the mechanical properties at ambient temperature. As the surfaces of RAs are covered with old mortar, the interfacial transition zones (ITZs) in RAC are significantly influenced. Compared to natural aggregate concrete (NAC), RAC has a higher void ratio (Xiao et al., 2018; Pradhan et al., 2020) and more number of internal microcracks (Koenders et al., 2014), causing its mechanical properties to be dramatically different. Therefore, strict design procedures are needed to control the structural production procedure of the RAC (Choi and Yun, 2012). Moreover, many concrete structures are easily damaged by fire during their service life, and the fire performance of the structure must be considered in relevant codes (ACI 216.1, 2007). Therefore, the fire performance of RAC should be further studied to promote its use. Previous research (Khoury, 2000; Sarhat and Sherwood, 2013) states that the difference in thermal expansion properties between the aggregates and mortar is vital for decreasing thermo-damage; the thermal expansion coefficient of RA is close to that of mortar and lower than that of NA. This statement has been verified by certain studies as well (Xiao et al., 2013; Meng et al., 2017; Xuan et al., 2017). Furthermore, Xuan et al. (2017) pointed out that RA can enhance the thermal properties of concrete. Xiao et al. (2013) also indicated that RAs have beneficial effects on the fire performance of concrete, especially with a large RA replacement ratio (more than 50%). Similarly, Meng et al. (2017) indicated that RAC with a large RA replacement ratio could enhance the fire performance of the concrete, and the optimal replacement ratio is 70%.

Besides, the rapid development of the automobile market is increasing the demand for rubber tires, which leads to an increasing amount of waste rubber. Based on the report from European Tyre and Rubber Manufacturer’s Association, 3.6 billion kilograms of waste rubber was produced in Europe in 2013 (Asaro et al., 2018). The effective utilization of waste rubber is also an urgent problem. Scholars (Gupta et al., 2014; Feng et al., 2018, 2019; Feng et al., 2021; Xie et al., 2019) found that rubber particles (RPs) made with waste tires can enhance the crack resistance and deformation capacity of concrete, namely, rubberized concrete. In addition, the toughness (Reda Taha et al., 2008) and service life of rubberized concrete (Graeff et al., 2012; Liu et al., 2013) are better than those of ordinary concrete. However, the influence of rubberized concrete on the fire performance of the concrete is relevant for consideration because the properties of the concrete are significantly weakened at high temperatures. Based on the vapor pressure theory (Choe et al., 2019), RPs soften and decompose at high temperature, which leads to an increasing number of pores in the concrete and decreases the internal steam pressure. Thus, the improvement in fire performance of the concrete using RPs has been verified by several scholars (Li et al., 2011; Mousa, 2017). Therefore, the RPs can also be incorporated into the RAC to form rubberized recycled aggregate concrete (RRAC). In addition to being made of green recyclable materials, the mechanical properties of RRAC are also excellent. Liu et al. (2015) found that RPs could enhance the fatigue performance of RAC. Moreover, the deformation capacity of RRAC was better than that of RAC under static (Chen et al., 2020) or impact loads (Li et al., 2016). However, few studies have focused on the thermo-mechanical performance of RRAC. Ganjian et al. (2009) reported that the properties of concrete varied significantly with more than 5% rubber content, and the toughness of RAC can be speculated to increase before the rubber softens and starts to decompose. In addition, the rubber decomposes or escapes through more number of pores in the RAC than the NAC at higher temperatures, thus releasing the internal steam pressure that further improves the high-temperature performance of the RAC.

It can be inferred from the above-mentioned research that adding a certain amount of rubber particles can effectively reduce the burst phenomenon of RAC. At present, there were few studies on the thermal-mechanical properties of RRAC, which did not focus on the stress-strain responses and microstructures of RRAC after exposure to high temperatures (Saberian et al., 2019). The mechanical properties of RRAC after heating at high temperatures including the optimal rubber content are necessary to be evaluated to further promote the use of RRAC. Thus, the purposes of this paper are to determine the mechanical properties of RRAC under high temperatures. Specifically, to investigate the thermal response as well as the residual mechanical properties after the high-temperature treatment. In careful consideration, large RA replacement ratios of 50 and 100% were used. The specimens were prepared with varying rubber contents (0, 5, 10, and 15%) and treated at different temperatures (25, 200, 400, and 600°C). The residual compression strength, deformation performance, stress–strain relationship, energy absorption capacity, and spalling mechanism of RRAC have been discussed. Finally, to further promote crumb rubber and recycled aggregate in the construction sector.

Experimental Arrangements

Mix Design and Carbon Emissions

Mix Design

Ordinary Portland cement with a compression strength of 42.5 MPa (P.O. 42.5R) was used. Continuous graded medium sand with a particle size of 0–4.75 mm, fineness modulus of 2.53, and an apparent density of 2,722 kg/m³ was used. In addition, coarse aggregates included NAs and RAs. The particle sizes of NAs and RAs were both 5–35 mm. RAs were mixed into the RAC by replacing equal volumes of NAs—three mix proportions constituting 0, 50, and 100% replacement of NA with RA. The apparent density and the crushing index of NA were 1,627 kg/m³ and 11.6%, and that of RA were 1,511 kg/m³ and 7.6%, respectively. Moreover, the rubber was mixed into the RAC as per 0, 5, 10, and 15% of the volume of sand. RPs were of 40-mesh size (approximately 0.425 mm) with an apparent density of 1,030 kg/m³. Besides, a type of superplasticizer of poly-carboxylic acid was employed.

The mix proportion is summarized in Table 1, where concise representations are used to distinguish the mix proportions based on preparation composition. RNAC represents rubberized natural aggregate concrete; A and B represent 50 and 100% replacement ratio of RA, and 5, 10, and 15 represent the replacement percentage of RPs. The slump of all groups is also summarized in Table 1, where an increase in the RA replacement rate exhibited a significant loss in the fluidity of the concrete owing to the strong absorption capacity of RAs. In addition, the fluidity of recycled concrete decreased continuously as the rubber content increasing, because the addition of rubber reduced the cohesion of the fresh mixture (Albano et al., 2005).

TABLE 1

TABLE 1. Mix proportion and slump of RNAC and RRAC.

Comparisons of Carbon Emissions

Increasing attention has been paid to the greenhouse gas emissions caused by concrete-like materials over the development of construction industrialization. According to the existing calculation method (Li and Chen, 2017; Xie et al., 2018), the total amount of carbon dioxide released from production E_u can be expressed as:

$E_u=m\times C_p(1)$

where C_p is the emission factor of raw materials—summarized in Table 2—referring to the results of numerous studies. The total carbon emissions of all groups are presented in Figure 1, which shows that the incorporation of RAs and RPs could effectually reduce carbon emissions to a certain extent. As the amount of sand reduced with the increasing rubber content, a slight decrease in emissions can be observed from Figure 1. Upon complete replacement of NAs with RAs, approximately 1 kg of carbon dioxide could be reduced in the process of producing 1 m³ of concrete. Therefore, RRAC was a type of low-carbon building material compared to ordinary concrete.

TABLE 2

TABLE 2. Cp of each type of raw materials for RRAC.

FIGURE 1

FIGURE 1. Carbon emissions of RNAC and RRAC.

Specimen Preparation and Heating Treatment

Specimen Preparation

All samples were removed from the molds after 24 h. Thereafter, the specimens were cured at a standard condition, where constant temperature of 20 ± 2°C and relative humidity of 95% for 28 days. The size, quantity, and heating temperature of all cylindrical specimens are summarized in Table 3. After heating at various temperatures, three temperatures of 200, 400, and 600°C were selected apart from the ambient temperature (25°C) to investigate the compressive behaviors of RRAC.

TABLE 3

TABLE 3. Arrangement of specimens.

Heating Treatment

A box-type electric furnace (SX2-28-13, China) was used for the high-temperature treatment, as shown in Figure 2. The furnace clearance size was 700 mm × 550 mm × 200 mm, rated power was 2 kW, maximum heating temperature was 1,000°C with a temperature controlling precision is ±1°C, and the heating element was a coarse-end type silicon-carbide rod. In addition, the distance between the specimen and the furnace wall is greater than 20 mm to ensure that the surface of the specimen was heated evenly. The heating rate in this investigation was set to 5°C/min (Li et al., 2011). Upon reaching the target temperature, a constant temperature was maintained for 60 min, after which the heating was stopped; the specimens were taken out and naturally cooled at almost room temperature. The mass of each specimen was measured before and after heating. Thus, the mass loss of the RRAC was calculated and the color change and crack development in the specimens were observed.

FIGURE 2

FIGURE 2. Photograph of the box type electric furnace.

Compression Testing Method

After heat treatments, as depicted in Figure 3, each flat surface of the cylinder were capped with a gypsum-leveling layer based on ASTM C617 (ASTM C617/C617M-15, 2015) before compression. Compression tests were carried out on a 4,000 kN universal testing machine (Matest C088-01, Italy). Based on the previous studies (Li et al., 2014; Guo et al., 2019), the loading rate on cylinders was uniformly constant to 0.18 mm/min. The longitudinal deformation of the cylinder was captured by using two linear variable differential transformers (LVDTs). Besides, two extra longitudinal strain gauges (BX120-10AA) were glued to corresponding positions of the specimen because of the low sensitivity of the LVDTs under small loads. Additionally, two more strain gauges (BX120-8AA) were utilized to capture the circumferential strain of the cylinder during the test. Moreover, the synchronous displacement and force signals were recorded through a strain collection device (JM3841, Jing Ming Technology Co., Ltd, China), which has an acquisition frequency of 1 Hz. The specimens were pre-pressed with a small load before the formal test to ensure the uniform compression of the cylindrical surface and observe the strain signals of two longitudinal strain gauges. The compression test was started after confirmation, and the test was finished when the load exceeded 20% of the peak stress. After that, the uniaxial compressive response including the stress−strain relationship, Young’s modulus E, uniaxial compression strength f_c [ASTM C39 (ASTM C39/C39M-20, 2020)], and Poisson’s ratio υ [ASTM C469 (ASTM C469/C469M-14, 2014)] could be obtained.

FIGURE 3

FIGURE 3. (A) Schematic diagram and (B) Test photo of the compression test.

Experimental Results

RRAC at Room Temperature

The effects of the recycled aggregate replacement ratio (0, 50, and 100%) and rubber particle content (0, 5, 10, and 15%) on the failure mode, stress–strain curve, compressive strength, modulus of elasticity, Poisson’s ratio, toughness, and specific toughness of RRAC were analyzed at room temperature without heating treatment.

Uniaxial Compression Strength and Elastic Properties

The experimental results of the compression strength and elastic properties, including Young’s modulus and Poisson’s ratio, are summarized in Table 4. As shown in Figure 4A, the compression strength of RRAC decreased slightly for specimens with higher RA replacement ratios. For instance, the compression strength was 3.82% lower than that of the natural aggregate concrete (RNAC-5) for a RA replacement ratio of 50% (RRAC-A-5). Similarly, the compressive strength for 100% RA replacement ratio (RRAC-B-5) was 9.38 and 5.77% lower than that of RNAC-5 and RRAC-A-5, respectively. Moreover, the addition of RPs reduced the compressive strength, and this effect was more evident for RRAC-B. For RA replacement ratios of 50 and 100%, the compression strength of RRAC with 5, 10, and 15% rubber content was 7.26, 8.53, 11.07, and 4.86, 11.38, and 19.47% lower than that of recycled concrete without rubber, respectively.

TABLE 4

TABLE 4. Experimental results of compression strength and elastic properties.

FIGURE 4

FIGURE 4. (A) Compression strength (B) Elastic modulus of RNAC and RRAC.

Considering the elastic properties, the content of rubber and replacement ratio of RA have little effect on Poisson’s ratio, which is stable at approximately 0.2. As shown in Figure 4B, the experimental results showed that for a RA replacement ratio of 50%, the elastic modulus of RRAC-A-5 was 2.95% lower than that of the natural aggregate concrete (RNAC-5), whereas the elastic modulus of recycled aggregate was 8.82% lower than that of RNAC-5 for RA replacement ratio of 100%. Moreover, the elastic modulus of RRAC with various rubber contents (5, 10, and 15%) decreased by 1.91, 5.69, and 9.32% for the same RA replacement ratio (50%), respectively. A similar trend was observed for 100% replacement rate of recycled aggregate. Therefore, the elastic modulus of RRAC decreased with an increase in the RA replacement ratio and rubber content.

Failure Modes

Typical failure modes of specimens after the uniaxial compression test are shown in Figure 5. The crack width was found to increase with the RA replacement rate, because, in contrast to NAC, RAC is comprised of five-phase media—NA, old mortar of RA, new mortar, old interfacial transition zone (ITZ) between old mortar and NA, and new ITZ between the new and old mortar (Lee and Choi, 2013). In addition, a large number of microcracks and pores were produced in the production process of RA owing to transport impacts (Nagataki et al., 2004; Tam et al., 2005). The strength of the new ITZ between the new and old mortar was reduced owing to the formation of a water film covering the surface of RA resulting from the high water absorption of RA. Furthermore, the crack growth developed along the weak zones of the RAC more easily. Therefore, an increase in the RA replacement ratio slightly reduced the compression strength of RRAC.

FIGURE 5

FIGURE 5. Failure modes: (A) Without heating treatment; (B) After 600°C heating treatment.

On the contrary, the number and width of the cracks decreased with the increase in the rubber content for the same RA replacement ratio, as shown in Figure 5. As concrete is a type of brittle material, cracks are usually generated through tensile strain when compression loads are applied. The RPs were used as soft materials to fill the microcracks and pores in the RAC; thus, the addition of rubber inhibited the expansion of a number of cracks and enhanced the defomation capacity of specimens.

Stress−Strain Relationship

The stress–strain curves of the RRAC are depicted in Figure 6, where Figure 6A illustrates that the stress–strain curves of RRAC are slightly different from those of RNAC. The falling section in the stress–strain curve of RRAC could be prolonged by mixing RPs, and a higher rubber content corresponded to a larger ultimate strain; therefore, the RPs could improve the deformation ability of RAC, as depicted in Figures 6B,C.

FIGURE 6

FIGURE 6. Stress−strain curves of RRAC: (A) 5% rubber content; (B) RRAC-A; (C) RRAC-B.

Energy Absorption Capacity

The area surrounded by the stress–strain curve represents the energy absorption of the specimens in the compression test. Several scholars have employed this method to evaluate the energy absorbing ability of concrete during the process of compression deformation. The specimen was close to failure in the later stage of stress unloading owing to the brittleness of the concrete material; thus, the strain corresponding to 20% peak stress (0.2f_c) was defined as the ultimate strain ε_u, as shown in Figure 7A. However, both RPs and RAs combinedly influenced the uniaxial compressive strength. Therefore, the energy absorption (EA) capacity of all specimens was normalized (NEA) with their compression strengths and are summarized in Table 5. In comparison to RNAC, the incorporation of RA reduced the energy absorption capacity of concrete. In addition, the energy absorption capacity of RRAC increased gradually with the rubber content, and it was unchanged for a rubber content less than 5%, as shown in Figure 7B. This phenomenon is consistent with existing results (Ganjian et al., 2009), which indicates that the performance of concrete cannot be evidently improved with small rubber content. In other words, more than 5% rubber content could enhance the toughness of RAC.

FIGURE 7

FIGURE 7. Calculation method and NEA of RRAC: (A) Calculation method of energy absorption; (B) NEA of RRAC under different rubber content.

TABLE 5

TABLE 5. Energy absorption (EA) and normalized energy absorption (NEA).

RRAC After Heated at High Temperature

Surface Observation

The door of the box resistance furnace manual opens when the internal temperature reaches a certain temperature to facilitate the observation of the phenomena occurring during the process at elevated temperatures. During the heating treatment, a small amount of water vapor began to escape beyond 100°C, and the steam escape was more evident when the temperature gradually increased to 160°C. In addition, the RPs started to melt and escape through the pores and cracks in the concrete, as shown in Figure 8A. The release of water vapor gradually decreased at elevated temperatures of 300°C, but a strong irritant smell still persisted because most of the RPs had melted. However, a small amount of steam still escaped from the edges of the furnace door upon attainment of the target temperature. The specimen was removed for practical observation after completion of the heating treatment.

FIGURE 8

FIGURE 8. (A) Melting rubber escaping through pores and cracks; (B) Spalling on the surface of RAC after high-temperature treatment (600°C).

The aggregate, mortar, and rubber in the concrete underwent a series of changes under high temperatures. From a macro level, these changes mainly depict the development of cracks and change in color of the cylindrical surface. At a high temperature of 600 C, numerous microcracks interlaced with each other and the lightest color of the specimens were observed; certain specimens without rubber modification (RAC-A and RAC-B) exhibited small areas of spalling on the surface, as illustrated in Figure 8B. Therefore, the experimental phenomena demonstrated that RPs could reduce the spalling of RAC.

Mass Loss

As explained earlier, the specimens were weighed before and after the heating treatment, m₀ and m₁, respectively. Moreover, the surfaces of the specimens were cleaned after the heat treatment. Thus, the mass loss, β, can be calculated as shown in Eq. 2. The results are summarized in Table 6. As shown in Figure 9A, the melting rubber broadened the escaping channel for internal water vapor. Therefore, the mass loss of RRAC increased with an increase in the rubber content. On the contrary, the mass loss of RNAC and RRAC was similar after heating treatment at 200 C under the same rubber content, as shown in Figure 9B. In comparison to RNAC after the heating treatment at 400°C, the mass loss for RRAC with 50% RA and 100% RA replacement ratio increased by 32.29 and 45.60%, respectively. The difference in mass loss between RRAC and RNAC was greater (35.03 and 58.50%, respectively) after heating treatment at 600°C. According to Failure Modes, there were more pores and microcracks in the RAC (Nagataki et al., 2004; Tam et al., 2005) to let water vapor escape.

$\beta =\frac{m_1-m_2}{m_0}\times 100\%(2)$

TABLE 6

TABLE 6. Mass loss for RRAC.

FIGURE 9

FIGURE 9. Effect of (A) Temperature and (B) RA replacement ratio on the mass loss of RRAC.

Residual Uniaxial Compression Strength

After the observation of the specimen surface and the measurement of mass loss, compression tests of all heated specimens were carried out using the universal testing machine. The uniaxial residual compression strength f_cr is listed in Table 7, where η represents the ratio of compression strength post heat treatment to that at ambient temperature (25°C). As shown in Figure 10A, after heating at 200, 400, and 600°C for a duration, the residual uniaxial compression strength of RRAC-A-5 was 33.28, 15.67, and 14.92% higher than that of RNAC-5. The pores in the RAs could provide the vapor escape channels at high temperatures to reduce the damage caused by internal vapor pressure, unlike that in RNAC. However, the defects of the aggregate itself adversely affect the ITZ of the concrete in case of high RA replacement ratios (100%). Therefore, the trend of η for RA replacement initially increased first but later declined.

TABLE 7

TABLE 7. Residual compression strength after heating.

FIGURE 10

FIGURE 10. Effect of (A) RA replacement ratio on η; rubber content on η for (B) RRAC-A and (C) RRAC-B.

On the contrary, the residual compression strength of concrete initially increased with the rubber content for 50% RA replacement rate (RRAC-A) but declined afterward, as shown in Figures 10B,C. The reason is that the RPs melted at high temperatures, which provided more channels to release the water vapor, thus reducing the internal damage and burst caused by the vapor pressure. Similar to RA, the porosity of a specimen with significant rubber content increased after the heat treatment owing to the melting of the rubber making the internal structure of concrete loose. The specimen with 100% RA replacement rate (RRAC-B) exhibited the highest porosity, and these small pores could easily connect to form larger pores after the rubber melted. Therefore, the porosity of concrete did not vary linearly with the heat resistance.

By conducting the multiple nonlinear regression (MNR) analysis, the value of η, as a function of target temperature T (°C) and rubber content ω (%) can be calculated by Eq. 3 proposed by Akbarzadeh Bengar et al. (Akbarzadeh Bengar et al., 2020):

$\eta =\frac{a-\left(bT+c\omega \right)}{1+dT-e\omega } \left(25\le T\le {600}^{°}\text{C};0\le \omega \le 15\%\right)(3)$

where a, b, c, d, and e are the undetermined coefficients, which are found as 1.022, 9.153 × 10^–4, 0.008, −1.391 × 10^–4, 0.008 for RRAC-A, 1.013, 1.190 × 10^–3, 0.005, −3.675 × 10^–4, 0.003 for RRAC-B, respectively. In addition, the fits of goodness (R²) for RRAC-A and RRAC-B are 0.991 and 0.941, respectively. In other words, this equation agrees well with the experimental data.

Residual Elastic Modulus

The residual elastic modulus is summarized in Table 8, where τ represents the ratio of the residual elastic modulus E_r at high temperatures to the elastic modulus at room temperature. As shown in Figure 11, the effect of rubber content on the elastic modulus of RRAC after heating beyond 400°C was smaller than that at room temperature, and the degradation of elastic modulus at a high temperature cannot be significantly reduced with addition of rubber.

TABLE 8

TABLE 8. Elastic modulus after heating treatment.

FIGURE 11

FIGURE 11. Loss of elastic modulus for RNAC and RRAC.

By conducting the MNR analysis, the value of τ, as a function of target temperature T (°C) and rubber content ω (%) can be calculated by:

$\tau =\frac{a-\left(bT+c\omega \right)}{1+dT-e\omega } \left(25\le T\le {600}^{°}\text{C};0\le \omega \le 15\%\right)(4)$

where a, b, c, d, and e are found as 1.051, 1.580 × 10^–3, −1.230 × 10^–3, 6.446 × 10^–4, 1.620 × 10^–3 for RRAC-A, and 1.061, 1.610 × 10^–3, 3.610 × 10^–3, 4.481 × 10^–4, 3.650 × 10^–3 for RRAC-B, respectively. In addition, the fits of goodness (R²) for RRAC-A and RRAC-B are 0.968 and 0.989, respectively. In other words, this equation agrees well with the experimental data.

Failure Modes

The failure modes of RRAC with different rubber contents and RA replacement ratios were observed to be similar; therefore, only the compressive failure modes beyond the 600°C heating treatment are shown in Figure 5B. The specimens experiencing a high temperature of 600°C exhibited cracks earliest in the loading process and suffered the most severe damage among others. The cracks were mainly developed along the interface between the aggregate and mortar. Thus, the cohesive force of the aggregate was significantly reduced leading to the collapse of the specimen in a large area.

Stress−Strain Curves

The compressive behaviors of all the specimens after the heat treatment were determined using the compression testing machine. Considering RRAC-A as an example, the stress–strain curves are plotted in Figure 12. The stiffness (slope of the rising phase of the curve) of all specimens treated at 200°C almost coincided with that of specimens treated at room temperature. The stiffness decreased as the heating temperature increased beyond 200°C, i.e., at 400 and 600°C, because of the melting temperatures are starting at around 160°C of the rubber as mentioned in Section 3.2.1. After heating at high temperatures, more microcracks and pores were produced in the concrete. Consequently, calcium hydroxide—the main part of the hydration products of concrete (Li et al., 2004)—started to decompose beyond temperatures of 400°C. These pores enhanced the deformation ability of the concrete resulting in extension of the ultimate strain limits of the stress–strain curves.

FIGURE 12

FIGURE 12. Typical stress−strain of RRAC-A after heating: (A) RAC-A; (B) RRAC-A-5; (C) RRAC-A-10; (D) RRAC-A-15.

Residual Energy Absorption Capacity

The values of EA and NEA can be calculated based on the stress–strain curves, as shown in Table 9. As shown in Figure 13, in contrast to the EA at room temperature, a higher temperature corresponded to a less concrete-toughening effect of the rubber owing to decomposition of rubber at high temperature; moreover, the NEA of RRAC remained stable for different rubber contents. Additionally, from the perspective of the RA replacement ratio, the effect of RPs on RRAC-B was more remarkable than that of RRAC-A. In other words, the rubber content should be increased with respect to the RA replacement ratio.

TABLE 9

TABLE 9. Energy absorption (EA) and normalized energy absorption (NEA) after heating.

FIGURE 13

FIGURE 13. Effect of rubber content on the NEA of (A) RRAC-A and (B) RRAC-B.

Constitutive Model for RRAC With Temperature and Rubber Content

Review of the Constitutive Model for RAC

As analyzed in Stress−Strain Relationship and Stress−Strain Curves, the constitutive curve of RAC was similar to that of ordinary concrete in terms of its geometric characters. One of the common constitutive models is illustrated in the Chinese standard GB50010 (GB/T 50010-2010, 2015), as shown in Eq. 5.

$\{\begin{array}{cc}y=a_0+a_{1}x+a_2{x}^2+a_3{x}^3& x\le 1\\ y=\frac{x}{b_0+b_{1}x+b_2{x}^2}& x>1\end{array}(5)$

where y = σ/f_c; σ is the uniaxial compression stress; f_c is the peak stress under uniaxial compression; x = ε/ε_c; ε is the strain under uniaxial compression; ε_c is the strain corresponding to the peak stress under uniaxial compression; a_i (i = 0,1,2,3) and b_j (j = 0,1,2) are the undetermined coefficients. The constitutive curve of concrete has some common features, as follows:

1)The curve starts at (0,0) when x = 0, y = 0.

2)The slope of the ascending segment of the curve decreases gradually without any inflection point for 0 ≤ x < 1, d²y/dx² < 0.

3)For x = 1, y = 1, and dy/dx = 0, the curve has only one peak point.

4)When x > 1, there is an inflection point (x₁, y₁) in the descending segment and d²y/dx² = 0.

5)When x > x₁, there is a maximum curvature point (x_2,y₂), d³y/dx³ = 0.

6)When x → ∞, y → 0, dy/dx → 0, which means that the descending curve is infinitely close to the X-axis but does not intersect.

7)For the entire curve, x is always greater than 0 and y is always between 0 and 1.

Therefore, the ascending and descending segments of the curve can be simplified based on these features and expressed as (Li et al., 2014):

$\{\begin{array}{cc}y=ax+\left(3-2a\right)x^2+\left(a-2\right)x^3& x\le 1\\ y=\frac{x}{b{\left(x-1\right)}^2+x}& x>1\end{array}(6)$

where a and b are the undetermined coefficients. Currently, there are relatively few studies on the stress–strain curves of RAC. Most of the fitting analysis of the curve focuses on concrete with different RA replacement rates at room temperature. Therefore, the constitutive models of RRAC-A and RRAC-B should be studied in variance of temperature and rubber content.

Constitutive Model for RRAC With Temperature and Rubber Content

Equation 6 was used for nonlinear fitting of the stress–strain curve of RRAC, and the undetermined coefficients were determined and summarized in Table 10. The goodness of fit (R²) was determined at above 0.9, thus verifying the suitability of this model for RRAC.

TABLE 10

TABLE 10. Parameters fitting of the constitutive model for RRAC.

Furthermore, the constitutive model of RRAC-A and RRAC-B can be integrated with different target temperatures and rubber contents using the parameters a and b, as expressed in Eqs. 7,8, where T (°C) and w (%) represent the target temperature and the rubber content, respectively. The fitting results are shown in Figure 14. Therefore, all the undetermined coefficients for RRAC-A and RRAC-B were evaluated in Eqs. 9, 11, 12, respectively. As there were only two RA replacement rates in this investigation and there was a certain dispersion of the stress–strain curve after the high-temperature damage, the unification of RRAC-A and RRAC-B was difficult. Thus, a larger size of additional test data including more number of RA replacement ratios are needed for further study.

$a=a_0+a_{1}T+a_{2}w+a_3{T}^2+a_4{w}^2+a_{5}wT(7)$

$b=b_0+b_{1}T+b_{2}w+b_3{T}^2+b_4{w}^2+b_{5}wT(8)$

$a=1.860-0.003T-0.091w-1.983\times {10}^{-7}{T}^2+0.006w^2+1.836\times {10}^{-6}wT(9)$

$b=1.700+0.009T-0.379w-2.889\times {10}^{-6}{T}^2+0.198w^2-2.601\times {10}^{-4}wT(10)$

$a=1.856-0.003T+0.020w-2.667\times {10}^{-6}{T}^2-0.002w^2+1.526\times {10}^{-4}wT(11)$

$b=1.219+0.008T+0.194w-9.747\times {10}^{-6}{T}^2-0.019w^2+1.177\times {10}^{-4}wT(12)$

FIGURE 14

FIGURE 14. Fitting results of RRAC: (A) a of RRAC-A; (B) b of RRAC-A; (C) a of RRAC-B; (D) b of RRAC-B.

Microstructure and Spalling Mechanism Analysis

RRAC Specimens at Ambient Temperature (25°C)

There were multiple microcracks between the rubber particle and mortar, as depicted in Figure 15A, indicating that the transition interface was relatively weak. Therefore, the compressive strength of the concrete weakened with the increase in rubber content. In addition, as shown in Figures 15A,B variety of cement hydration products was observed in the cementing materials, among which there were numerous ettringite formation (AFt), and a compact structure was formed to connect the surrounding products. Moreover, a small amount of calcium hydroxide (CH) was observed, and microcracks developed along the weak interface between the mortar and aggregate.

FIGURE 15

FIGURE 15. Microstructure of RRAC: (A) and (B) 25°C; (C) and (D) 200°C; (E) and (F) 400°C; (G) and (H) 600°C.

RRAC Specimens After Heated at 200°C for 60 min

As shown in Figure 15C, RPs only softened and did not decompose after heating at 200°C; therefore, there was no noticeable change in morphology. In addition, cracks had developed along the weak interface. Compared with the samples at ambient temperature, the cracks were longer and wider at higher temperatures, indicating that the damage inside the concrete was more extensive owing to heating. Further, Figure 15D confirms the absence of AFt in RRAC at high temperatures because AFt had completely decomposed at 200°C. However, calcium silicate hydrate (C-S-H) and CH were not decomposed at this temperature. Therefore, the positive influence of the RRAC was relatively small after heating at 200°C.

RRAC Specimens After Heated at 400°C for 60 min

As depicted in Figure 15E, since almost all RPs have been decomposed, no RPs can be found at 400°C. Several holes are formed in the place initially occupied by the cracking and escaping rubber in the cementitious paste. As depicted in Figure 15F, there was an adverse change in the microstructure of the specimen, and the amount of cement hydration products (such as AFt and CH) had dramatically reduced. The cement hydration products decomposed into acicular calcium silicate and flocs.

RRAC Specimens After Heated at 600°C for 60 min

As shown in Figure 15G, few holes were still present in the microstructure by the RPs after heating at 600°C, but the damage of concrete caused by this high temperature was the most severe among all the cases. In addition, these holes provided space for the development of cracks that penetrated each other to form even larger cracks. As shown in Figure 15H, only few radial hydration products were present, which were the residual hydration products of mortar after decomposition at high temperatures. In addition, these radial hydration products led to radial cracks in the ITZ.

Spalling Mechanism Under Elevated Temperatures for RRAC

A large amount of water evaporated from the cement paste at temperatures below 400°C, and all kinds of hydration products decomposed successively. Although the pressure inside the structure increased according to the vapor pressure theory, the internal pores and the escaping of RPs released the space within the structure. In other words, the internal vapor pressure was effectively released from the dense concrete structure under the influence of the increased rubber content that created more space. On the contrary, almost all the hydration products of the cement decomposed and the crystal water escaped from the aggregate upon reaching 600°C. Simultaneously, the mismatch responses between aggregates and mortar led to thermal stresses in the ITZ owing to the thermal expansion of materials. Although a high rubber content released a large amount of space under elevated temperatures and provided a buffer to the steam pressure, the load capacity was decreased owing to the relatively loose internal structure of RRAC compared to that of ordinary concrete. Therefore, the rubber content should not be too high considering the strength and spalling resistance of RRAC.

Conclusion

Uniaxial compressive tests on RRAC specimens with two RA replacement rates (50 and 100%), three rubber contents (0, 5, 10, and 15%), and four temperatures (25, 200, 400, and 600°C) were conducted to explore the properties of the concrete media. The RRAC was found as a suitable alternative to the RAC for use in structures requiring fire resistance. The following conclusions can be drawn from the investigation:

RRAC is a type of low-carbon building material compared to ordinary concrete, where the CO₂ emissions slightly decrease because the amount of sand is reduced with a higher rubber content in the mix. Approximately 1 kg of carbon dioxide can be reduced in the process of producing one cubic concrete upon complete replacement of NAs with RAs.

Between the completion of heat treatment and performing the compression test, a small area of spalling was observed on the surface of certain specimens, except for the rubberized specimens. In addition, the melting rubber broadened the escaping channel for releasing the internal water vapor. Therefore, the mass loss of RRAC increased with an increase in rubber content.

With an increase in temperature, the effect of rubber content on the elastic modulus of RRAC was smaller than that at room temperature. Consequently, more number of microcracks and pores were produced in the concrete after heating at high temperatures beyond 400°C. These pores enhanced the deformation ability of concrete and extended the ultimate strain limit of the stress–strain curves.

Unlike the energy absorption capacity at room temperature, the toughening effect of rubber on concrete was lessened at higher temperatures owing to the decomposition of rubber at such temperatures.

Empirical models were proposed to reflect the effects of high temperature and rubber contents on the stress–strain relationship of RRAC.

Based on the microstructure analysis using SEM, numerous pores were observed that facilitated the release of internal vapor through the cracking and escaping rubber. Moreover, the RPs could reduce the spalling of specimens based on the vapor pressure theory. Thus, RRAC with 10% rubber was recommended on considering the factors of uniaxial compressive strength, energy absorption capacity, and spalling resistance.

Scope for Future Research

1) There are limit data about the stress-strain relations of RRAC under the elevated temperatures. One of our future works is to summarized more experimental data from other papers to obtained a more precisely model about stress-strain curves with temperature and rubber content.

2) Using TGA or EDS, XRD analysis to capture the variation on the C-S-H, CH and CaCO₃ under different high-temperature treatment.

Data Availability Statement

The original contributions presented in the study are included in the article/Supplementary Material, further inquiries can be directed to the corresponding authors.

Author Contributions

YT was responsible for experiment scheme design, test execution, and data analysis. WF was responsible for writing the original manuscript and theoretical guidance. ZC was responsible for experiment scheme guidance and manuscript revision. YN, MY, and JL were responsible for participating in test execution and data analysis.

Funding

This research was funded by the National Natural Science Foundation of China (Grant No. 12032009,51578162).

Conflict of Interest

The authors declare that the research was conducted in the absence of any commercial or financial relationships that could be construed as a potential conflict of interest.

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