Influence of Decoupled Charge Structure and Filler on the Blasting Effect

This study compared models of specimens with diﬀerent ﬁller media and decoupled charge structures in terms of the blasting eﬀect. The test system combined a high-speed camera and high-speed static strain test analyzer. A physical model of a concrete single-borehole decoupled charge structure was designed to study the geometric elements of the blasting funnel, ﬂyrock launch velocity, peak strain values, and distribution of the gravel lumpiness. The experimental results showed that for the same decoupling coeﬃcient, when expandable polystyrene foam (EPS) was used as the ﬁlling medium, the radius, depth, and volume of the blasting funnel of the model specimen were larger, the ﬂyrock launch velocity was slower, the peak stress of the specimen was higher, and the distribution of gravel lumpiness was more even. The relationship between the experimental index and the decoupling coeﬃcient follows the changing trend of ﬁrst increasing and then decreasing or ﬁrst decreasing and then increasing. With air and EPS as the ﬁlling media, the concrete model specimens could achieve optimal blasting eﬀects at decoupling coeﬃcients of 1.83 and 1.69, respectively. The results conﬁrm the feasibility and practicability of using EPS as a ﬁller and can provide guidance and an experimental basis for the selection of the decoupling coeﬃcient and ﬁlling medium in blasting engineering.


Introduction
Drilling and blasting can efficiently crush rock media and are used in civil applications such as mining [1][2][3] and tunnel construction [4,5]. e blasting fracture of rock can be viewed as the result of a synergistic effect of the blasting stress wave and the quasistatic pressure of the blasting gas. e blasting stress wave is the main cause of rock fracture, while the blasting gas further expands the cracks [6][7][8]. Efficient energy use to achieve the desired blasting effect has been extensively researched. e properties of the rock, type of explosive, initiation method, borehole layout, and charge structure all affect the blasting result; however, the charge structure is the most important factor [9].
Foster first proposed achieving directional fracture of rock using detonation energy from blasting to act on the axial groove of the drilling borehole over a hundred years ago. Limited by the theory and construction techniques, the proposed technology of changing the charge structure [10] could not be implemented. Since their proposal in 1940, air-decoupled charge structures have been applied in many countries, achieving economic benefits in mines, water conservancy, highways, and other fields [11]. Segmented charges were later used in production, such as in the Chinese Anshan Iron and Steel Mine and the Anhui Phoenix Mine [12]. Charge structures can now be divided into coupled and decoupled charges, continuous charges, and interval charges. Decoupled charges can be further distinguished as radial, axial, and radial-and-axial structures. Water or other filling media are used in decoupled charge structures [11][12][13]. Different charge structures have varying influences on the energy transfer, borehole pressure, explosive stress field, and blasting effect of explosives; smooth blasting, presplit blasting, and other controlled blasting methods typically adopt decoupled charge structures [14].
A decoupled charge structure can effectively avoid excessive fragmentation of rocks around the borehole, ensure utilization of the blasting energy, and achieve the best blasting effect [15]. us, decoupled charge structures have been shown to perform better than coupled charge structures in engineering practice. e decoupling coefficient and filling medium [16][17][18][19][20][21][22][23][24][25] are the main factors contributing to the blasting effect. Experiments performed by Gu et al. [16] on the decoupling coefficient showed that a water-decoupled charge structure could effectively taper the instantaneous vibrational energy, resulting in a higher average crushing rate of the rock and less harmful dust. ey also demonstrated the relationship between different charge structures and the corresponding rock impedance, noting that there was an optimal decoupling coefficient. Lei et al. [17] conducted comparative tests on low-permeability coal seams with three charge groups having different shapes and decoupling coefficients. When the radial decoupling coefficient was 1.5, the stress wave with a lower main frequency had the strongest stimulation effect on the coal body. Under the joint action of the blasting stress wave and detonation gas, the gas extraction rate in low-permeability coal seams can be increased by a factor of 2.0-3.4. e influence of the decoupling coefficient on explosive crack growth was studied in laboratory experiments and confirmed through numerical simulations by Wang et al. [18]. At a decoupling coefficient of 1.67, the blasting effect of a slotted charge is best. e crack growth speed and dynamic stress intensity factor decrease with vibration and reach a small peak in the middle and late stages of crack growth. A decoupled charge structure weakened the intensity of the initial blasting stress wave, and either water or mortar as a filler reduced the dissipation of the blasting energy, as demonstrated by Jiang et al. [19] for carbonate rock using ANSYS/LS-DYNA software. is result was confirmed in a comparative study of air and water by Wang et al. [20], who found that the energy dissipation was caused by excessive fragmentation of the surrounding rock by the blasting shock wave, which was limited with the use of a water filler. Yang et al. [21] investigated the impact of the filling medium and decoupling coefficient on the evolution of the blasting stress in decoupled charge blasting. With an increase in the decoupling coefficient, the blasting stress attenuation index initially increased and then decreased. In addition, numerical simulation results showed that in decoupled charge blasting, the filling medium reduced the pressure of the borehole, and the peak stress of the borehole wall was lowest when the decoupling coefficient was 2.5-3.5.
While a decoupled charge structure can improve the blasting effect, the blasting requirements vary with different environments and fillers [17,26]. e state of research on decoupling coefficients currently consists of studies that have been previously performed, in many cases a long time ago. Owing to the anisotropy of rock materials and the experimental data collected, the analytical results vary too significantly to be predictive [27]. e authors selected a suitable model material, concrete, to derive more controlled and reliable data. To date, most studies on filling media have focused on natural materials such as air, water, sand, and soil [28,29]. Few studies have been conducted using polymers (e.g., expandable polystyrene foam (EPS)). Using EPS in combination with a decoupled charge structure can provide the following unique advantages [29,30]: (1) EPS is solid and extremely light. us, no auxiliary device is needed to position the explosive in the borehole. (2) EPS can dissipate the stress wave to assist in decreasing the decoupling coefficient appropriately. (3) EPS can meet special requirements such as those for eccentric decoupled blasting and can control the vibration.
An appropriate selection of the decoupling coefficient and filling medium is important to improve the blasting effect.

Experimental System.
A physical model of a concrete single-borehole decoupled charge blasting system was designed, and a test system combining a high-speed camera with a high-speed static strain tester was used. e following aspects were considered: (1) e angles of the geometric elements of the blasting funnel. e feasibility and practicability of the use of EPS as a filling medium for a decoupled charge structure are confirmed, and these results can provide reliable theoretical guidance and an experimental basis for selection of the decoupling coefficient and filling medium in blasting engineering. e authors studied the relationship between the decoupled charge structure and the blasting effect and designed a test system combining a high-speed camera and a high-speed static strain test analyzer with a synchronous control system (PC 1, PC 2, and an EF-500A-type highenergy pulse detonator). e instrument layout for the field experiments is shown in Figure 1, and the relevant experimental system is shown in Figure 2.
A high-speed camera (5KF10, Hefei Fuhuang Junda High-Tech Information Technology Co., Ltd., China) that can provide 1 million pixels, 3500 frames of shooting capability, and full-frame resolution (1280 × 860 pixels) for 4000 fps high-frame-rate images was used. e pixel size is 14 μm × 14 μm. e machine memory is 16 GB; 4 GB of images can be acquired per second, leading to an accuracy of 0.01 μs.
A high-speed static strain test analyzer (DH3820, Jiangsu Donghua Testing Technology Co., Ltd., China) combined with a foil resistance strain gauge sensor (BX120-20AA, Beijing Yiyang Yingzhen Testing Technology Co., Ltd., China) was used to collect data on the strain changes in the concrete model. e high-speed static strain test analyzer has a variable range of ±50000 με and a maximum continuous sampling rate of 100 Hz/channel. e instrument is small, easy to use, and suitable for many environments, both indoors and out. e foil resistance strain gauge sensor has a sensitivity coefficient of 2.08 ± 0.01 Ω, a base size of 26 mm × 6 mm, and a sensitive column size of 20 mm × 3 mm, does not require any welding for use, and can detect a maximum microstrain of 20000 με. e self-contained insulated wire has a length of 20 cm and can be crimped to a custom conductor with a length of 0.2 cm to 2 m. e synchronous control system was completed by a computer terminal and detonating device. e startup sequence and delay time of the detonation, shooting, and acquisition were defined, and control is possible to the microsecond. e high-speed camera and high-speed static strain test analyzer controlled by the computer terminal simultaneously photographed and measured the strain in the model specimens. Blasting tests were carried out in good lighting and stable exposure conditions.

Experimental Design
Boreholes in rock and rock-like materials will produce a large number of random cracks under a blast load, even with minimal amounts of explosive. ese experiments aimed to study the impact of different filler media with varying decoupling coefficients on the blasting effect. e model material used was concrete, as this was expected to demonstrate the effects most successfully. Small concrete models constructed based on the blasting similarity criterion functioned as representative specimens. Concrete is convenient, economical, safe, and somewhat protective of the engineering site. e model specimen was a single-borehole charge containing 0.5 g diazodinitrophenol (DDNP) with a special small electric detonator measuring 6 mm × 44 mm. It was detonated by the high-voltage discharge of an EF-500A high-energy pulse initiator. Table 1 lists the relevant parameters of the concrete model specimen, and Table 2 lists the relevant parameters of the special electric detonator. e model test piece was made of ordinary standard Portland cement (with a strength grade of 42.5 MPa), sand, gravel, and water, which were mixed and stirred at a mass ratio of 1 : 1.556 : 3.158 : 0.52 and then maintained for 28 d at a temperature of 20 ± 2°C and relative humidity of 60% ± 5%. e experimental model had a geometric similarity ratio of CL � 0.1, and 30 concrete models with dimensions of 300 × 300 × 300 mm were produced based on the blasting similarity criterion, as shown in Figure 3. With the same method, three cylinders with a bottom diameter of 50 mm and a height of 100 mm were prepared to investigate the physical and mechanical properties of the model specimens, as shown in Figure 4.
A borehole was predrilled to a depth of 60 mm in the center of the specimen. Six specimens were prepared for each of the borehole diameters, d B � 8, 10, 12, 14, and 16 mm. As only the decoupled charge structure was studied, the effects of five different decoupling coefficients on the blasting effect of air and EPS were explored. e EPS used in these experiments and its related material parameters are presented in Figure 5 and Table 3, respectively. As shown in Figure 6, the diameter was d A � 6 mm, and the borehole diameter varied as d B � 8, 10, 12, 14, and 16 mm. e effects of air and polystyrene foam on the blasting effect were studied, and the corresponding decoupling coefficients were α A � α B � 1.33, 1.67, 2, 2.33, and 2.67.

Geometric and Dynamic Elements of the Blast.
e experimental procedure to determine the blast geometry and speed was as follows: (1) ree concrete specimens with borehole diameters d B � 8 mm were used. One utilized the air-decoupled charge structure; the other two specimens used the EPS-decoupled charge structure. e specimens were charged and filled.
(2) e high-speed camera was placed 3 m from the specimen and connected and powered on along with computer 1, and the collection parameters were defined (see Figure 2). (3) Once the personnel had been evacuated to the bunker, the detonation was started. e high-speed camera acquired images in a controlled fashion. (4) After the blast, the main geometric elements of the blasting funnel, including the blasting funnel radius, depth, and volume, were measured and recorded. e data from the high-speed camera were saved, the collection parameters were reset, and the next test was started. (5) Steps 1 through 4 were repeated for concrete specimens with diameters d B � 10, 12, 14, and 16 mm.
After the data collection, the data were sorted and analyzed.  (1) ree concrete specimens with borehole diameters d B � 8 mm were used. One utilized the air-decoupled charge structure; the other two specimens used the EPS-decoupled charge structure. e specimens were charged and filled.         Shock and Vibration

Strain Peak Tests and
(2) A foil resistance strain gauge sensor was tangentially attached to the top of the test piece at a distance of 12 cm from the center of the borehole. e highspeed static strain test analyzer and computer 2 were connected and powered on, and the parameters were defined (see Figure 2).
(3) Once filled, the three model specimens were covered with a flexible protective cover to prevent the scattering and secondary crushing of fragments after the explosion. Once the personnel had been evacuated to the bunker, the detonation was carried out, and the static strain analyzer collected high-speed stressstrain data for the model specimen. (4) After the blast, the gravel in the flexible protective sleeve was collected, the block sizes of the gravel were classified using sieves with apertures of 10, 15, 20, 25, 30, and 40 mm, and the percentage of each fraction was calculated and recorded. e data were collected by the high-speed static strain tester, the collection parameters were reset, and the next test was started. (5) Steps 1 through 4 were repeated for concrete specimens with diameters d B � 10, 12, 14, and 16 mm. After data collection was completed, the data were sorted and analyzed.
Two BX120-20AA strain gauges were bonded to the front surface of 15 concrete models in radial and tangential directions with superglue. e distance between the measurement point center and the center of the borehole was 12 cm, and the strain data for the concrete model specimens were collected by the static strain test analyzer. According to the experimental blasting scheme, 15 concrete models were tested for blasting and strain. Zero drift elimination and calibration of the instrument was required before each model test piece was tested.

Geometric Elements of the Blasting Funnel.
e geometric elements of the blasting funnel, i.e., its radius, depth, and volume, were used to evaluate the blasting effect. irty groups of data for each index were obtained in the blasting experiments, with three groups for each index. To facilitate data processing and analysis, averages of the three data groups were taken to represent the index. e results for postblast indices of geometric elements were recorded, as listed in Table 4. e relationships between the mean radius, depth, and volume of the blasting funnel and the decoupling coefficient were plotted using the data in Table 4, as shown in Figures 7(a)-7(c), respectively. e relationship between the radius of the blasting funnel and the decoupling coefficient is shown in Figure 7(a). e radius of the blasting funnel initially increases and then decreases with an increase in the decoupling coefficient, which indicates that there is an optimal decoupling coefficient in the actual decoupled charge structure. In the decoupled charge structures with air and EPS as the filling media, the radius of the blasting funnel reached the maximum values with α A � 1.8-2.0 and α P � 1.7-1.9, respectively. e decoupling coefficients were not in the same range, indicating that the influence of the two filling media on the blasting effect was inconsistent. e blasting funnel radius reached the optimal value for the air-decoupled charge structure at α A � 1.90, and the EPS-decoupled charge structure was optimal at α P � 1.76. e variations in the depth of the blasting funnel (Figure 7(b)) and volume of the blasting funnel (Figure 7(c)) with the decoupling coefficient were similar to that of the blasting funnel radius (Figure 7(a)). Both initially increased and then decreased with an increase in the decoupling coefficient. is indicates that there were decoupling coefficients that corresponded to the optimal depth and volume of the blasting funnel in the actual decoupled charge structure. In the decoupled charge structure with air and EPS, when α A � 1.8-2.0 and α A � 1.5-1.8, the depth and volume of the blasting funnel reached the maximum values, respectively. When α A � 1.87 and 1.90 and α P � 1.54 and 1.75, the depth and volume of the blasting funnel reached the optimal values, respectively.
In the air-decoupled charge structure, a decoupling coefficient of 1.89 yielded the optimal values for each index of the blasting funnel. In the EPS-decoupled charge structure, the optimal value of the decoupling coefficient was 1.68.
is shows that the EPS-decoupled charge structure can   In case of the EPS-decoupled charge structure, excessive pulverization of the near-field rock can be avoided by prolonging the action time of the blasting stress wave and the explosive gas, changing the specific gravity of the energy distribution, and using more blasting energy for crushing.

Flyrock Launch Velocity.
e postblasting process can be divided into three stages: the stress wave tensile failure stage, explosive gas expansion crack stage, and the flyrock launch velocity stage. Only the flyrock launch velocity in the third stage was analyzed in these experiments by organizing and analyzing the data collected by the high-speed camera. e average value of the three flyrock launch velocities indicates the actual condition of the decoupled charge structure model specimens.
e flyrock launch velocities of the model specimens after blasting are summarized in Table 5. e variations in the flyrock launch velocity with the decoupling coefficient of the flyrock were plotted based on the results in Table 5. As shown in Figure 8, with the increase of the uncoupling coefficient, the flyrock launch velocity   decreases first and then increases. e flyrock launch velocity initially decreases and then increases with an increase in the decoupling coefficient, and the variation trends for the two curves are the same.
is indicates that there is a decoupling coefficient that optimizes the flyrock launch velocity in the actual decoupled charge structure.
For the same decoupling coefficient, the concrete model with the EPS-decoupled charge structure had a more moderate flyrock launch velocity after blasting was completed. A slower flyrock launch velocity could be obtained at a lower decoupling coefficient, as seen in Figure 8. e main reason for this phenomenon is that EPS is denser than air and has low compressibility. e energy of the explosive energy is transmitted to the distant rock medium; therefore, the explosive energy transmitted to the flyrock is lower, reducing the flyrock launch velocity. In the two decoupled charge structures, the minimum flyrock launch velocities occurred at α A � 1.75-1.95 and α P � 1.51-1.61. e optimal decoupling coefficients were α A � 1.80 and α P � 1.56.

Peak Strain Values of the Specimens.
e radial, tangential, and mean strain data collected by the DH3820 system are summarized in Table 6.
From the five sets of radial decoupled charge blasting strain data results obtained in the tests, the relationships between the radial, tangential, and average strain and the decoupling coefficient are shown in Figure 9. e radial and tangential peak strains initially increased and then decreased with an increase in the decoupling coefficient, as shown in Figure 9. is indicates that there is an optimal decoupling coefficient that can maximize the strain in the experimental model. With the same decoupling coefficient, the peak radial, tangential, and mean strains of the EPS-decoupled charge structure are higher than those of the air-decoupled charge structure. When the decoupling coefficient and filling medium are the same, the radial peak strain is greater than the tangential peak strain, and the model specimen with the EPS-decoupled charge structure exhibits a higher peak strain at a lower decoupling coefficient. e corresponding peak strain is at its maximum when the radius and depth of the blasting funnel volume are at their maximum, as seen in Figures 7(a)-7(c) and Figure 9.
For the air-decoupled charge structure, the maximum peak strain appears at α A � 1.80-1.95, and the optimal decoupling coefficient is 1.88. For the EPS-decoupled charge structure, the maximum peak strain appears at α P � 1.55-1.85, and the optimal decoupling coefficient is 1.80. For the same peak strain, the decoupling coefficient of the EPS-decoupled charge structure is smaller, indicating that the required drilled diameter is smaller. For the same decoupling coefficient, the peak strain of the EPS-decoupled charge structure is larger, which indicates that the blasting energy has a greater effect on the model specimens with the EPSdecoupled charge structure.

Distribution of Gravel Lumpiness.
e degree of rock lumpiness after blasting is often used to evaluate the blasting effect. e gravel in the flexible protective sleeves was collected after the blasting and classified using sieves with apertures of 10,15,20,25,30,35, and 40 mm. e percentage of gravel in each grade was calculated. e cumulative distributions of gravel lumpiness in each grade are shown in   e degree of fragmentation after blasting was analyzed with the G-G-S distribution function. K 50 and K 80 were used to evaluate the blasting effect. e G-G-S distribution function is expressed as follows: where y is the cumulative percentage of gravel under a certain sieve grade (%), x is the block size of the gravel (mm), x 0 is the largest piece of gravel (mm), n is a distribution parameter, and the numerical values of distribution parameters n, K 50 , and K 80 are obtained via a regression method. e statistical analysis of the gravel block size distribution is given in Table 8.
e relationships between the maximum gravel sizes, K 50 , K 80 , and the decoupling coefficient of the specimens after blasting are plotted based on the data in Table 8, as shown in Figures 10(a) and 10(b). e maximum gravel size initially decreased and then increased with an increase in the decoupling coefficient for the two decoupled charge structures, as shown in Figure 10(a). e EPS-decoupled charge structure had the maximum gravel size, which appeared at a smaller decoupling coefficient. us, the higher the decoupling coefficient of the air-decoupled charge structure, the larger the maximum gravel size of the model specimens.
e K 50 and K 80 index values of the EPS-decoupled charge structure are smaller than those of the air-decoupled charge structure, and the gravel lumpiness is more evenly distributed, as seen in Figure 10(b). e blasting effect of the EPS-decoupled charge structure is better than that of the airdecoupled charge structure. In the model specimens with the air-decoupled charge structure, the value of K 50 varies from 40.22 to 83.81 mm. e size of the gravel is large, and the distribution is less concentrated. In the model specimens with the EPS-decoupled charge structure, the value of K 50 varies from 31.20-44.39 mm, which is a large variation. e size of the gravel is smaller and the distribution is more even.
It can also be concluded that for the model specimens with different decoupled charge structures, the values of K 80 vary from 59.42-116.91 mm and 45.40-75.39 mm, respectively, and the distribution trends are similar to the those for K 50 , indicating that the energy of the explosive with the EPSdecoupled charge structure is more even. By avoiding the formation of crushing areas near the rock source, more explosive energy can be transferred to the rock medium in the distant source. e maximum gravel size and K 50 and K 80 show a changing trend of decreasing first and then increasing with the increase of the decoupling coefficient, as shown in Figures 10(a) and 10(b). us, there is an optimal decoupling coefficient to achieve the desired blasting effect. In the model specimens with the air-decoupled charge structure, when α A � 1.80, the minimum value of K 50 is 40.22 mm, and the  optimal decoupling coefficient is 1.73. In the model specimens with the EPS-decoupled charge structure, when α P � 1.61, the minimum value of K 50 is 31.20 mm, and the optimal decoupling coefficient is 1.66. For K 80 , the minimum values of the air-decoupled and EPS-decoupled charge structures are 59.42 and 45.40 mm, respectively, and the optimal decoupling coefficients are 1.95 and 1.75, respectively. e comparison of the experimental results for the model specimens with two types of decoupled charge structures shows that the EPS-decoupled charge structure can effectively improve the distribution of gravel lumpiness and improve the utilization of explosive energy.   6. Discussion e decoupling coefficients and the filling media have a significant impact on the blasting effect. Air and EPS have the same cushioning effect. However, different decoupling coefficients and filling media can result in different blasting effects and energy distributions. e experimental results are discussed and analyzed from the perspectives of the decoupling coefficients, filling media, and transmission and loss of blasting energy in this section.

Decoupling Coefficients.
e decoupling coefficient strongly affected the blasting effect and energy transfer. With a small decoupling coefficient, the explosive energy acted almost directly on the borehole and formed a compressive crushing zone. e energy dispersed to distant areas was lessened, and the phenomenon of a high block rate was likely to occur. With a large decoupling coefficient: (i) e blast stress wave was transmitted for too long in the filling medium. (ii) Much of the explosive energy was consumed in the medium. (iii) e excess explosive energy acted on the borehole. (iv) e distant blasting area was unable to achieve the expected blasting effect.
In model experiments with two decoupled charge structures, when α A � 1.89 and α P � 1.75, the radius, depth, and volume of the model blasting funnel reached the maximum values (see Figures 7(a)-7(c)).
When the decoupled coefficients were α A � 1.80 and α P � 1.56, the flyrock launch velocities of the model specimens reached the minimum values (see Figure 8). With α A � 1.88 and α P � 1.80, the peak values of the blasting stress in the model specimens were the highest (see Figure 9). When α A � 1.73 and α P � 1.66, the maximum size of the gravel was at a minimum (see Figure 10(a)). erefore, in the decoupled charge structure for the same rock type and explosive type, there was a specific decoupling coefficient that optimized the blasting effect.
Under the joint action of the blasting stress wave and blasting gas, the experimental results and decoupling coefficient show the changing trend of first increasing and then decreasing or first decreasing and then increasing, which indicates that the decoupling coefficient is an important factor influencing the blasting effect. In these experiments, the radius, depth, volume, and peak stress of the blasting funnel of the model specimens were optimal when the air-decoupled charge was equal to α A � 1.83. With EPS as the filling medium and a decoupling coefficient α P � 1.69, the initial flyrock launch velocity, maximum block size, and block rate of the model specimens were optimal. us, there was a specific decoupling coefficient that optimized the blasting effect.
Moreover, the decoupling coefficient was related to the type and nature of the filling medium. e blasting effect could be optimized with the selection of the filling medium and decoupling coefficient.

Filling Medium.
In the blasting tests of model specimens with different filling media, the radius, depth, volume, and peak value of the obtained blasting funnel initially increased and then decreased with an increase in the decoupling coefficient (see Figures 7(a)-7(c)). e flyrock launch velocity and maximum flyrock block size initially decreased and then increased with an increase in the decoupling coefficient (see Figures 8 and 10(a)). It was found that the decoupled charge structure with EPS could increase the peak burst stress for a decoupling coefficient in the range of 1.75 < α < 2.05 (see Figure 9), which is similar to the research reported by Yang et al. [21] (2.5 < α < 2.35), but the decoupling coefficient range is different. Yang et al. [21] chose a polycarbonate material (with a modulus of elasticity of 4.548 GPa, Poisson's ratio of 0.321, and density of 1449 g/ cm 3 ) and concrete (modulus of elasticity of 24.5 GPa, Poisson's ratio of 0.23, and density of 2100 g/cm 3 ) as the model specimen materials; the different physical parameters of the two model specimens resulted in a difference in the range of the decoupling coefficient.
Owing to the high density of EPS, its compressibility was small and yielded better energy transfer. After the explosion, the gas in the polystyrene foam expanded more rapidly than that in the air, thereby reducing the flyrock launch velocity (see Figure 8). e EPS resulted in a more uniform and lower pressure on the borehole, which reduced the excessive pulverization around the borehole, avoided a high block rate, effectively improved the block distribution of the gravel, and made the utilization of the explosive energy more uniform and reasonable (see Table 8 and Figures 10(a) and  10(b)).
Comparing and analyzing the results of the two decoupled charge structure blasts, the blasting effect of the concrete model specimens with the EPS-decoupled charge structure was better. e optimal blasting effect could be obtained at a smaller decoupling coefficient. e authors recommend reducing the diameter of the borehole to save engineering costs. e EPS-decoupled charge structure has many engineering advantages; there is no need for an auxiliary device to fix the position of the explosive in the borehole, which can reduce complicated construction links and achieve an ideal blasting effect in some blasting environments with special requirements. e type of filling medium and decoupling coefficient can most effectively impact the blasting energy transfer characteristics.

Blasting Energy Transfer and
Loss. EPS can be characterized as a lightweight material with strong shock absorption and high mechanical strength. Its self-shock period is long, which delays the blasting stress action time. Compared with a coupled charge structure, the decoupled charge structure prevents the blasting shock wave from directly acting on the borehole and transmits more blasting energy to a greater distance, thus achieving the best blasting effect. e energy transfer losses stemmed from the lower compressibility of EPS; thus, the explosion in EPS was much lower than that in air. With EPS as the filling medium, the energy consumed by deformation is less than that with air as the medium. e breaking energy not used on the rock is much lower than that with air. Because air has a high compression rate, much of the explosive energy is consumed by the compression of the air.

Conclusions
e effects of the filling medium and the decoupling coefficient on the blasting effect were investigated from the perspective of energy transfer and loss. In these experiments, concrete puckering decoupled blasting physical models were considered and a high-speed camera combined with a highspeed static strain testing analyzer was used. e authors then analyzed the geometric elements of the blasting funnels in the model specimens after blasting, the flyrock launch velocity, the peak strain of the specimens, and the distribution of the gravel lumpiness. e filling medium had a significant effect on the blasting. e experimental results showed that the decoupled charge structure with EPS had a profound influence on the blasting effect in the concrete models.
At the same decoupling coefficient, for the EPSdecoupled charge structure, (i) e radius, depth, and volume of the blasting funnel were larger. (ii) e flyrock launch velocity was slower. (iii) e peak stress peak of the specimen was higher. (iv) e distribution of gravel was more even.
EPS is denser than air and much less compressible, which allowed for a more even pressure and a prolonged shock wave for an overall better energy transfer. ere was less pulverization around the borehole, a lower block rate, improved block distribution, and better utilization of the explosive energy. e decoupling coefficient significantly impacted the blasting effect, and there is a specific decoupling coefficient that could lead to an optimal blasting effect. e decoupling coefficient and the type and nature of the filling medium had an enormous influence on the blasting effect. e optimal decoupling coefficient for the air-decoupled charge structure was 1.83, whereas that of the EPS-decoupled charge structure was 1.69. e optimal blasting effect can be obtained by using EPS as the filling medium with a small decoupling coefficient. e tests qualitatively compared the explosion effects of model specimens with different filling media and decoupling coefficients.
e theoretical analysis and quantitative calculations were insufficient and obvious. Although five different decoupling coefficients were used in the experiments, the optimal decoupling coefficient for different decoupled charge structures was found only by curve fitting, which was limited by the cost of materials; thus, experimental calculation of the optimal decoupling coefficient was not performed. Specific experimental verification of the calculated optimal decoupling coefficient and a more in-depth study of the transfer of explosive energy with different charge structure conditions are the main directions for future research.

Data Availability
e data used to support the findings of this study are available from the corresponding author upon request.

Conflicts of Interest
e authors declare that there are no conflicts of interest regarding the publication of this paper.